Research Article Calculation of Reaction Forces in the ...
Transcript of Research Article Calculation of Reaction Forces in the ...
Research ArticleCalculation of Reaction Forces in the Boiler SupportsUsing the Method of Equivalent Stiffness of Membrane Wall
Josip SertiT DraDan Kozak and Ivan SamardDiT
Mechanical Engineering Faculty in Slavonski Brod Trg Ivane Brlic-Mazuranic 2 35 000 Slavonski Brod Croatia
Correspondence should be addressed to Josip Sertic josipserticsfsbhr
Received 29 August 2013 Accepted 29 December 2013 Published 15 May 2014
Academic Editors S Kou and K-L Ou
Copyright copy 2014 Josip Sertic et al This is an open access article distributed under the Creative Commons Attribution Licensewhich permits unrestricted use distribution and reproduction in any medium provided the original work is properly cited
The values of reaction forces in the boiler supports are the basis for the dimensioning of bearing steel structure of steam boiler Inthis paper the application of the method of equivalent stiffness of membrane wall is proposed for the calculation of reaction forcesThemethod of equalizing displacement as themethod of homogenization of membrane wall stiffness was applied On the exampleof ldquoMilanordquo boiler using the finite element method the calculation of reactions in the supports for the real geometry discretized bythe shell finite element was made The second calculation was performed with the assumption of ideal stiffness of membrane wallsand the third using themethod of equivalent stiffness of membrane wall In the third case themembrane walls are approximated bythe equivalent orthotropic plateThe approximation of membrane wall stiffness is achieved using the elasticity matrix of equivalentorthotropic plate at the level of finite element The obtained results were compared and the advantages of using the method ofequivalent stiffness of membrane wall for the calculation of reactions in the boiler supports were emphasized
1 Introduction
Nowadays the steam boilers of waste incineration powerplants are made specifically according to the requirementsof investors Due to the location where the boiler will beset up the amount and type of fuel to be burned in agiven time and technical parameters of produced steamthe production of steam boilers is mainly individual Thisrepresents an exceptional effort for the designers The pipesand sheet metal are the basic structural elements used formaking boilers Larger structural units called the membranewalls are obtained by welding these elementsThemembranewalls make the basic structure of boiler and have a doublefunction The heat exchanger that is evaporator is theprimary function and the secondary is transfer of loadingThe steam boiler membrane walls are loaded by the pressureof working fluid (watersteam) their ownmass and the massof other structural units that rely on the membrane walls themass of working fluid the mass of insulation and refractoryand the foulingmass that is deposited during the combustionprocessThe loading is transferred across themembranewallsto the boiler supports and then to the bearing steel structure
Since the water tube boilers are large structures consistingof a large number of pipes connected to the membrane wallsit is very difficult to accurately calculate the reactions in thesupports In practice there are two approaches to calculatethe reactions in the steam boiler supports The first approachis based on the assumption that themembrane stiffness of theboiler membrane wall is very high so the boiler is calculatedas an ideal rigid bodyThe second approach takes into accountthe finite stiffness of the membrane walls using the finiteelementmethodThe discretization of real geometry of boiler(membrane walls) requires an extremely large number offinite elements so this approach is rarely used eventuallyfor smaller boilers Most often the membrane wall stiffnessis approximated by the equivalent stiffness of orthotropicplateshell which allows a multiple reduction of degrees offreedom of a numerical model
It is difficult to find more detailed research papers onthe topic of homogenization of steam boiler membranewall In 2012 Milosevic-Mitic [1] with a group of authorsproposed a procedure for calculating the strength of watertube boiler using the finite element of orthotropic plate
Hindawi Publishing Corporatione Scientific World JournalVolume 2014 Article ID 392048 12 pageshttpdxdoiorg1011552014392048
2 The Scientific World Journal
The homogenization ofmembrane wall stiffness is performednumerically using the method of equalizing displacement
When calculating the deflection of membrane walls dueto the influence of underpressureoverpressure of flue gasesthe equivalent wall thicknessmethod ismost commonly usedin practice The bending stiffness of membrane wall pipe isequal to the bending stiffness of equivalent wall thickness forthe axis perpendicular to the longitudinal axis of membranewall pipe and the bending stiffness of membrane wall tapeis equal to the bending stiffness of equivalent wall thicknessfor the axis parallel to the longitudinal axis of membrane wallpipe
The steam boiler membrane wall represents a structurallyorthotropic plate The stiffened plates that are frequentlyused both in building and in the processingpower plantswhere it is necessary to achieve the optimal structuralsolution considering the mass of structure also belong tothis class of structures The earliest research on the topicof stiffness of stiffened plates was most likely done byHuber [2ndash4] His investigations were inspired by the lackof exact expressions for solving the problems of bendingand buckling of stiffened structures by using the theoryof homogeneous orthotropic plates Similarly Flugge [5]published the first paper on the topic of structurally stiffenedshell in 1932 and 15 years later so did van der Neut [6]Over time the understanding of the theory of deformation ofstructurally orthotropic plates and shells has progressed Theterms ldquoequivalent stiffnessrdquo and ldquoequivalent wall thicknessrdquobecame the basis for the analysis of deformation of stiffenedor structurally orthotropic platesshells Furthermore Daleet al [7] applied the equivalent stiffness in the researchof buckling of pressure loaded sandwich plates Smith etal [8] proposed an improved formulation that takes intoconsideration the change of position of the neutral surfacethat is connected with the local interaction between theplate and stiffener Pfluger [9] Gomza and Seide [10] andLibove and Hubka [11] applied in their research the methodof equivalent stiffness and thickness of stiffened plateshellIn the papers [12ndash14] the theory of symmetric sandwichplates with the included transverse shear stiffness is appliedIn 1956 Huffington Jr [15] analyzed the equivalent stiffnessof orthogonally stiffened plate without the stiffener eccen-tricity During the last fifty years the equivalent plate orshell approach was still being used as a first approxima-tion method [16ndash19] For the experimental determinationof elasticity constants the method of testing the load-deformation characteristics of repeating structural part of thestructurally orthotropic plate was most commonly used [20]In 1969 Soong [21ndash23] presented a derivation of the stiffnessexpressions for orthotropic cylinders based on a deformationenergy approach Throughout the following years specialattention was given to the interaction between the plate andstiffeners [24] for a different layout or grid of stiffeners [25ndash27] and different combinations of loads In 1995 Jaunky etal [28 29] presented a refined smeared-stiffener theory forgrid-stiffened laminated-composite panels based upon thework presented by Smith et al [8] Similarly Wodesenbetpresented an improved smeared-stiffener theory for grid-stiffened laminated-composite cylinders in 2003
It can be concluded that the current research is mainlybased on two systematic analytical methods that take ordo not take into account the transverse shear stiffnessFirst there is a direct equilibrium-compatibility methodThe first method uses equilibrium and compatibility in adirect manner for plates reinforced by stiffeners The secondone is called the basic-cell energy-equivalence method Thesecond method is based on defining the equivalence betweenthe deformation energy of the basic repeating cell and thedeformation energy of the equivalent orthotropic plate Thismethod is suitable for the determination of the members ofelasticity matrix for grid-stiffened plates and sandwich plates
Unlike the stiffened plates a steam boiler membrane wallconsists of a homogeneous plate with attached stiffenersTherefore the two mentioned methods are not entirelysuitable for the determination of equivalent stiffness ofmembrane wall that is the equivalent elasticity constantsThe process of homogenization of steam boiler membranewall is presented in the papers [30ndash32] The elasticity con-stants for the membrane and bending stiffness of mem-brane wall are determined theoretically by equalizing thedeformation of membrane wall with the deformation ofequivalent orthotropic plate In these papers the transverseshear stiffness is not taken into consideration
2 Steam Boiler Membrane Wall asthe Structurally Orthotropic Plate
The steam boiler membrane wall can be approximated asthe equivalent orthotropic plate that is the orthotropicplate which will have the same elastic properties as the realmembrane wall Using Kirchhoff-Love theory of shells [3334] the constitutive equations of equivalent orthotropic plateor shell can be written as follows
120590 = D sdot 120576 (1)
where 120590 is vector of section forces D is matrix of elasticityand 120576 is vector of deformation According to [35] it can besaid that the constitutive equations for the analysis of platesand shells are analogThematrix expression (1) represents thesix constituent equations ofmembranewall as the structurallyorthotropic plate or its equivalent orthotropic plate whichconnect the section forces with the corresponding deforma-tions
[
[
[
[
[
[
[
[
1198731
1198732
11987312
1198721
1198722
11987212
]
]
]
]
]
]
]
]
=
[
[
[
[
[
[
[
[
11986011
11986012
0 0 0 0
11986022
0 0 0 0
11986033
0 0 0
11986311
11986312
0
sym 11986322
0
11986333
]
]
]
]
]
]
]
]
sdot
[
[
[
[
[
[
[
[
1205761
1205762
12057612
1205811
1205812
2 sdot 12058112
]
]
]
]
]
]
]
]
(2)
11987311198732 and119873
12are the section forces (Figure 1) and119872
11198722
and11987212are the sectionmoments (Figure 2) in themembrane
wall that is the equivalent orthotropic plate 11986011 11986012 11986022
and 11986033
are the members of elasticity matrix for membraneloads and 119863
11 11986312 11986322 and 119863
33are the members of
The Scientific World Journal 3
N12N12N21 N21N1
N1N2 N2
120572212057221205721 1205721
AmAp
Am equivAp
Figure 1 Section forces in the membrane wall that is the equivalent orthotropic plate with the membrane stiffness of membrane wall A119898
equivalent to the membrane stiffness of orthotropic plate A119901
M2
M1M12M21
120572212057221205721 1205721
DmDp
DmequivDp
M2M21 M1
M12
Figure 2 Section moments in the membrane wall that is the equivalent orthotropic plate with the bending stiffness of membrane wallD119898
equivalent to the bending stiffness of orthotropic plateD119901
elasticity matrix for bending loads of equivalent orthotropicplate 120576
1 1205762 and 120576
12are the membrane deformations and 120581
1
1205812 and 120581
12are the curvatures of neutral surface of structurally
orthotropic plate that is the equivalent orthotropic plateThe members of elasticity matrix referring to the mem-
brane stiffness [30 34] of membrane wall can be calculatedusing the following expressions
11986011
=
1198641198981
sdot ℎ
1 minus ]11989812
sdot ]11989821
11986012
=
1198641198982
sdot ℎ sdot ]11989812
1 minus ]11989812
sdot ]11989821
11986022
=
1198641198982
sdot ℎ
1 minus ]11989812
sdot ]11989821
11986033
= 11986611989812
sdot ℎ
(3)
where1198641198981
is modulus of elasticity for themembrane stiffnessin the direction of axis 120572
1(the axis parallel to the axis of
pipe in the membrane wall) 1198641198982
is modulus of elasticity forthe membrane stiffness in the direction of axis 120572
2(the axis
perpendicular to the axis of pipe in themembrane wall) ]11989812
is Poissonrsquos ratio for the membrane stiffness in the directionof axis 120572
1 ]11989821
is Poissonrsquos ratio for the membrane stiffnessin the direction of axis 120572
2 and 119866
11989812is shear modulus for
the membrane stiffness The members of elasticity matrix
referring to the bending stiffness [29 33] of membrane wallcan be calculated using the following expressions
11986311
=
1198641198871
sdot ℎ
3
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986312
=
1198641198872
sdot ℎ
3sdot ]11988712
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986322
=
1198641198872
sdot ℎ
3
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986333
=
11986611988712
sdot ℎ
3
12
(4)
where the elasticity constants for the bending stiffness areindicated by index 119887 The expression for the wall thicknessof equivalent orthotropic plate [30] can be obtained fromthe equality of moment of inertia of the cross-section ofmembrane wall considering the plane perpendicular to thelongitudinal axes of the membrane pipes (Figure 3) and thecross-section of equivalent orthotropic plate Consider
ℎ =radic
3 sdot 120587
16 sdot 119863 sdot 119896
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) +
(119896 minus 119863) sdot 119905
3
119863 sdot 119896
(5)
4 The Scientific World Journal
h
k
120601D times 120575
1205722
1205722
1205723
1205723
t
b2
Membrane wallkmdashstep of pipe in the
Equivalent orthotropic platehmdashwall thickness of the equivalent orthotropic plate
membrane wall
Figure 3 Geometry of cross-section of membrane wall and equivalent orthotropic plate
1
2
3
4
5
6
7
8
9
10
11
25
24
23
22
21
20
19
18
17
16
15
14
13
12
X
Y
Z
Figure 4 Real calculation geometry model
The Scientific World Journal 5
850
2500
2100
1925
1030
1080
4915
1790
890
11701440
X
Y
Z
1980
Figure 5 Calculation geometry model approximated as the equivalent orthotropic plate (dimensions are in mm)
The elasticity constants of equivalent orthotropic platefor the membrane stiffness can be calculated using theanalytical expressions suggested in the paper [31 32] Theseexpressions are obtained by equalizing the deformations ofmembrane wall and equivalent plate (thickness ℎ) with theequivalent membrane load
1198641198981
=
119864
119896 sdot ℎ
[
120587
4
sdot (119863
2minus (119863 minus 2 sdot 120575)
2) + (119896 minus 119863) sdot 119905]
1198641198982
=
119896 sdot 119864
ℎ sdot [3 sdot (119863120575 minus 1)
3sdot (1205878 minus 1120587) + 119887119905]
11986611989812
asymp
radic1198641198981
sdot 1198641198982
2 sdot (1 +radic]11989812
sdot ]11989821
)
]11989821
= ]11989812
sdot
1198641198982
1198641198981
(6)
where119864 is modulus of elasticity and ]11989812
= ] is Poissonrsquos fac-tor for the isotropic material of membrane wall The expres-sions for the elasticity constants of equivalent orthotropicplate and for the bending stiffness of membrane wall areproposed in the paper [31 32] Same as for the membranestiffness these expressions are also obtained by equalizing
6 The Scientific World Journal
Figure 6 3D-disposition of biomass incineration power plant ldquoMilanordquo
the deformations of membrane wall and equivalent plate(thickness ℎ) with the equivalent bending load
1198641198871
=
119864
119896 sdot ℎ
3sdot [
3 sdot 120587
16
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) + (119896 minus 119863) sdot 119905
3]
1198641198872
= 119864 sdot (
119905
ℎ
)
3
sdot
(119899 sdot 119896)
4
sum
119899
119894=1(119894 sdot 119896)
4minus (119894 sdot 119896 minus 119887)
4
11986611988712
asymp
radic1198641198871
sdot 1198641198872
2 sdot (1 +radic]11988712
sdot ]11988721
)
]11988721
= ]11988712
sdot
1198641198872
1198641198871
(7)
where 119899 is number of pipes in the membrane wall and ]11988712
=
] is Poissonrsquos factor for the isotropic material of membranewall After the homogenization of steam boiler membrane
wall the stiffness matrix of shell element can be calculatedaccording to the expression
k = int
119860
B119879DB 119889119860 (8)
where 119860 is surface of shell element and B is operator ofboundary magnitude
3 Calculation of Reactions in the Steam BoilerSupports for a Real Model of MembraneWall Geometry for the MembraneWalls Approximated by the EquivalentOrthotropic Plate and for the Ideal RigidModel of Boiler Geometry
Thefinite element method using Abaqus 69-3 will be appliedfor the calculation of reactions in the supportsThe real geom-etry of membrane walls (Figure 4) and the membrane wallsapproximated as the equivalent orthotropic plate (Figure 5)
The Scientific World Journal 7
360
100
2120
100
2120
100
100
1035118013851315
1 2 3 4 5
1740
Superheater 1
Superheater 2
Superheater 3
(SH 1)
(SH 2)
(SH 3)
Seco
nd p
ass
Firs
t pas
s
Third
pas
s
A
A
A
A
Evaporator(EV)
Figure 7 Position of boiler supports and heat exchangers (dimensions are in mm)
will be discretized by a four-node doubly curved thin shellelement using the reduced integrationwith hourglass controlThe finite element has the codename S4R5 and it is applied forsmall deformations and has five degrees of freedom per node
The load of the mass of boiler structure will be taken intoconsideration for the calculation of reactions in the supportsof ldquoMilanordquo steam boiler (Figure 6) Other loads such as themass of working fluid the fouling mass that is depositedon the heating surfaces during the combustion process
the mass of refractory and the mass of insulation will not beconsidered here Pipematerial ofmembranewalls is P235GHmaterial of membrane tape and buckstays is S235JRG2 andmaterial of chambers is 16Mo3 All three steels belong tothe group of low-carbon steels with le 03 carbon Sincethe boiler membrane walls are evaporator heating surfacesthe calculation temperature is 120599 = 275
∘C Assuming thatthe mechanical properties of boiler structure are isotropic[36] the modulus of elasticity for all three materials is
8 The Scientific World Journal
Table 1 List of positions according to Figure 4
Pos Type Dimensions Pos Type Dimensions
1 Shell and end of drum 1206011200 times 35mm 14 Collector header ofside wall 1206011397 times 125mm
2 Downcomers 1206011683 times 16mm 15 Collector header ofrear wall of third pass 1206011397 times 125mm
3 Connecting pipe 120601889 times 88mm 16 Side wall of secondpass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 12
4 Collector header ofrear wall of first pass 1206011397 times 125mm 17 Rear wall of second
pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
5 Front wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
18 Side wall of third pass
Pipe 120601483 times 45mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 15
6 Side wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 21
19 Rear wall of third pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
7 Rear wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
20 Buckstays HE-B120
8 Collector header ofwall of hopper 1206011397 times 125mm 21
Distributor header ofrear wall of second
pass1206011397 times 125mm
9 Connecting pipes 120601483 times 4mm 22 Wall of hopper
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
10 Distributor header ofside wall 1206011683 times 20mm 23 Distributor header of
rear wall of first pass 1206011397 times 125mm
11 Distributor header offront wall 1206011397 times 125mm 24 Distributor header of
wall of hopper 1206011397 times 125mm
12Collector header offront and rear wall of
second pass1206011397 times 125mm 25 Distributor header of
rear wall of third pass 1206011397 times 125mm
13 Side wall in transitionzone
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 34
approximately equal and amounts to 119864 = 18712GPa For thevalue of Poissonrsquos factor ] = 03 is used
Due to the single boiler symmetry for the calculationusing the finite element method it is sufficient to model onlyone-half of the boiler geometry (Figures 4 and 5) The boileris supported by ten supports five on the distributor chamber
of the left side wall and five on the distributor chamber of theright side wall (Figure 7) In the third pass of the boiler theheat exchangers were installed that is one evaporator andthree superheaters The heat exchangers were supported onthe side walls of the third pass Due to the weight of heatexchangers the load of the left and right side wall of the third
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
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2 The Scientific World Journal
The homogenization ofmembrane wall stiffness is performednumerically using the method of equalizing displacement
When calculating the deflection of membrane walls dueto the influence of underpressureoverpressure of flue gasesthe equivalent wall thicknessmethod ismost commonly usedin practice The bending stiffness of membrane wall pipe isequal to the bending stiffness of equivalent wall thickness forthe axis perpendicular to the longitudinal axis of membranewall pipe and the bending stiffness of membrane wall tapeis equal to the bending stiffness of equivalent wall thicknessfor the axis parallel to the longitudinal axis of membrane wallpipe
The steam boiler membrane wall represents a structurallyorthotropic plate The stiffened plates that are frequentlyused both in building and in the processingpower plantswhere it is necessary to achieve the optimal structuralsolution considering the mass of structure also belong tothis class of structures The earliest research on the topicof stiffness of stiffened plates was most likely done byHuber [2ndash4] His investigations were inspired by the lackof exact expressions for solving the problems of bendingand buckling of stiffened structures by using the theoryof homogeneous orthotropic plates Similarly Flugge [5]published the first paper on the topic of structurally stiffenedshell in 1932 and 15 years later so did van der Neut [6]Over time the understanding of the theory of deformation ofstructurally orthotropic plates and shells has progressed Theterms ldquoequivalent stiffnessrdquo and ldquoequivalent wall thicknessrdquobecame the basis for the analysis of deformation of stiffenedor structurally orthotropic platesshells Furthermore Daleet al [7] applied the equivalent stiffness in the researchof buckling of pressure loaded sandwich plates Smith etal [8] proposed an improved formulation that takes intoconsideration the change of position of the neutral surfacethat is connected with the local interaction between theplate and stiffener Pfluger [9] Gomza and Seide [10] andLibove and Hubka [11] applied in their research the methodof equivalent stiffness and thickness of stiffened plateshellIn the papers [12ndash14] the theory of symmetric sandwichplates with the included transverse shear stiffness is appliedIn 1956 Huffington Jr [15] analyzed the equivalent stiffnessof orthogonally stiffened plate without the stiffener eccen-tricity During the last fifty years the equivalent plate orshell approach was still being used as a first approxima-tion method [16ndash19] For the experimental determinationof elasticity constants the method of testing the load-deformation characteristics of repeating structural part of thestructurally orthotropic plate was most commonly used [20]In 1969 Soong [21ndash23] presented a derivation of the stiffnessexpressions for orthotropic cylinders based on a deformationenergy approach Throughout the following years specialattention was given to the interaction between the plate andstiffeners [24] for a different layout or grid of stiffeners [25ndash27] and different combinations of loads In 1995 Jaunky etal [28 29] presented a refined smeared-stiffener theory forgrid-stiffened laminated-composite panels based upon thework presented by Smith et al [8] Similarly Wodesenbetpresented an improved smeared-stiffener theory for grid-stiffened laminated-composite cylinders in 2003
It can be concluded that the current research is mainlybased on two systematic analytical methods that take ordo not take into account the transverse shear stiffnessFirst there is a direct equilibrium-compatibility methodThe first method uses equilibrium and compatibility in adirect manner for plates reinforced by stiffeners The secondone is called the basic-cell energy-equivalence method Thesecond method is based on defining the equivalence betweenthe deformation energy of the basic repeating cell and thedeformation energy of the equivalent orthotropic plate Thismethod is suitable for the determination of the members ofelasticity matrix for grid-stiffened plates and sandwich plates
Unlike the stiffened plates a steam boiler membrane wallconsists of a homogeneous plate with attached stiffenersTherefore the two mentioned methods are not entirelysuitable for the determination of equivalent stiffness ofmembrane wall that is the equivalent elasticity constantsThe process of homogenization of steam boiler membranewall is presented in the papers [30ndash32] The elasticity con-stants for the membrane and bending stiffness of mem-brane wall are determined theoretically by equalizing thedeformation of membrane wall with the deformation ofequivalent orthotropic plate In these papers the transverseshear stiffness is not taken into consideration
2 Steam Boiler Membrane Wall asthe Structurally Orthotropic Plate
The steam boiler membrane wall can be approximated asthe equivalent orthotropic plate that is the orthotropicplate which will have the same elastic properties as the realmembrane wall Using Kirchhoff-Love theory of shells [3334] the constitutive equations of equivalent orthotropic plateor shell can be written as follows
120590 = D sdot 120576 (1)
where 120590 is vector of section forces D is matrix of elasticityand 120576 is vector of deformation According to [35] it can besaid that the constitutive equations for the analysis of platesand shells are analogThematrix expression (1) represents thesix constituent equations ofmembranewall as the structurallyorthotropic plate or its equivalent orthotropic plate whichconnect the section forces with the corresponding deforma-tions
[
[
[
[
[
[
[
[
1198731
1198732
11987312
1198721
1198722
11987212
]
]
]
]
]
]
]
]
=
[
[
[
[
[
[
[
[
11986011
11986012
0 0 0 0
11986022
0 0 0 0
11986033
0 0 0
11986311
11986312
0
sym 11986322
0
11986333
]
]
]
]
]
]
]
]
sdot
[
[
[
[
[
[
[
[
1205761
1205762
12057612
1205811
1205812
2 sdot 12058112
]
]
]
]
]
]
]
]
(2)
11987311198732 and119873
12are the section forces (Figure 1) and119872
11198722
and11987212are the sectionmoments (Figure 2) in themembrane
wall that is the equivalent orthotropic plate 11986011 11986012 11986022
and 11986033
are the members of elasticity matrix for membraneloads and 119863
11 11986312 11986322 and 119863
33are the members of
The Scientific World Journal 3
N12N12N21 N21N1
N1N2 N2
120572212057221205721 1205721
AmAp
Am equivAp
Figure 1 Section forces in the membrane wall that is the equivalent orthotropic plate with the membrane stiffness of membrane wall A119898
equivalent to the membrane stiffness of orthotropic plate A119901
M2
M1M12M21
120572212057221205721 1205721
DmDp
DmequivDp
M2M21 M1
M12
Figure 2 Section moments in the membrane wall that is the equivalent orthotropic plate with the bending stiffness of membrane wallD119898
equivalent to the bending stiffness of orthotropic plateD119901
elasticity matrix for bending loads of equivalent orthotropicplate 120576
1 1205762 and 120576
12are the membrane deformations and 120581
1
1205812 and 120581
12are the curvatures of neutral surface of structurally
orthotropic plate that is the equivalent orthotropic plateThe members of elasticity matrix referring to the mem-
brane stiffness [30 34] of membrane wall can be calculatedusing the following expressions
11986011
=
1198641198981
sdot ℎ
1 minus ]11989812
sdot ]11989821
11986012
=
1198641198982
sdot ℎ sdot ]11989812
1 minus ]11989812
sdot ]11989821
11986022
=
1198641198982
sdot ℎ
1 minus ]11989812
sdot ]11989821
11986033
= 11986611989812
sdot ℎ
(3)
where1198641198981
is modulus of elasticity for themembrane stiffnessin the direction of axis 120572
1(the axis parallel to the axis of
pipe in the membrane wall) 1198641198982
is modulus of elasticity forthe membrane stiffness in the direction of axis 120572
2(the axis
perpendicular to the axis of pipe in themembrane wall) ]11989812
is Poissonrsquos ratio for the membrane stiffness in the directionof axis 120572
1 ]11989821
is Poissonrsquos ratio for the membrane stiffnessin the direction of axis 120572
2 and 119866
11989812is shear modulus for
the membrane stiffness The members of elasticity matrix
referring to the bending stiffness [29 33] of membrane wallcan be calculated using the following expressions
11986311
=
1198641198871
sdot ℎ
3
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986312
=
1198641198872
sdot ℎ
3sdot ]11988712
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986322
=
1198641198872
sdot ℎ
3
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986333
=
11986611988712
sdot ℎ
3
12
(4)
where the elasticity constants for the bending stiffness areindicated by index 119887 The expression for the wall thicknessof equivalent orthotropic plate [30] can be obtained fromthe equality of moment of inertia of the cross-section ofmembrane wall considering the plane perpendicular to thelongitudinal axes of the membrane pipes (Figure 3) and thecross-section of equivalent orthotropic plate Consider
ℎ =radic
3 sdot 120587
16 sdot 119863 sdot 119896
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) +
(119896 minus 119863) sdot 119905
3
119863 sdot 119896
(5)
4 The Scientific World Journal
h
k
120601D times 120575
1205722
1205722
1205723
1205723
t
b2
Membrane wallkmdashstep of pipe in the
Equivalent orthotropic platehmdashwall thickness of the equivalent orthotropic plate
membrane wall
Figure 3 Geometry of cross-section of membrane wall and equivalent orthotropic plate
1
2
3
4
5
6
7
8
9
10
11
25
24
23
22
21
20
19
18
17
16
15
14
13
12
X
Y
Z
Figure 4 Real calculation geometry model
The Scientific World Journal 5
850
2500
2100
1925
1030
1080
4915
1790
890
11701440
X
Y
Z
1980
Figure 5 Calculation geometry model approximated as the equivalent orthotropic plate (dimensions are in mm)
The elasticity constants of equivalent orthotropic platefor the membrane stiffness can be calculated using theanalytical expressions suggested in the paper [31 32] Theseexpressions are obtained by equalizing the deformations ofmembrane wall and equivalent plate (thickness ℎ) with theequivalent membrane load
1198641198981
=
119864
119896 sdot ℎ
[
120587
4
sdot (119863
2minus (119863 minus 2 sdot 120575)
2) + (119896 minus 119863) sdot 119905]
1198641198982
=
119896 sdot 119864
ℎ sdot [3 sdot (119863120575 minus 1)
3sdot (1205878 minus 1120587) + 119887119905]
11986611989812
asymp
radic1198641198981
sdot 1198641198982
2 sdot (1 +radic]11989812
sdot ]11989821
)
]11989821
= ]11989812
sdot
1198641198982
1198641198981
(6)
where119864 is modulus of elasticity and ]11989812
= ] is Poissonrsquos fac-tor for the isotropic material of membrane wall The expres-sions for the elasticity constants of equivalent orthotropicplate and for the bending stiffness of membrane wall areproposed in the paper [31 32] Same as for the membranestiffness these expressions are also obtained by equalizing
6 The Scientific World Journal
Figure 6 3D-disposition of biomass incineration power plant ldquoMilanordquo
the deformations of membrane wall and equivalent plate(thickness ℎ) with the equivalent bending load
1198641198871
=
119864
119896 sdot ℎ
3sdot [
3 sdot 120587
16
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) + (119896 minus 119863) sdot 119905
3]
1198641198872
= 119864 sdot (
119905
ℎ
)
3
sdot
(119899 sdot 119896)
4
sum
119899
119894=1(119894 sdot 119896)
4minus (119894 sdot 119896 minus 119887)
4
11986611988712
asymp
radic1198641198871
sdot 1198641198872
2 sdot (1 +radic]11988712
sdot ]11988721
)
]11988721
= ]11988712
sdot
1198641198872
1198641198871
(7)
where 119899 is number of pipes in the membrane wall and ]11988712
=
] is Poissonrsquos factor for the isotropic material of membranewall After the homogenization of steam boiler membrane
wall the stiffness matrix of shell element can be calculatedaccording to the expression
k = int
119860
B119879DB 119889119860 (8)
where 119860 is surface of shell element and B is operator ofboundary magnitude
3 Calculation of Reactions in the Steam BoilerSupports for a Real Model of MembraneWall Geometry for the MembraneWalls Approximated by the EquivalentOrthotropic Plate and for the Ideal RigidModel of Boiler Geometry
Thefinite element method using Abaqus 69-3 will be appliedfor the calculation of reactions in the supportsThe real geom-etry of membrane walls (Figure 4) and the membrane wallsapproximated as the equivalent orthotropic plate (Figure 5)
The Scientific World Journal 7
360
100
2120
100
2120
100
100
1035118013851315
1 2 3 4 5
1740
Superheater 1
Superheater 2
Superheater 3
(SH 1)
(SH 2)
(SH 3)
Seco
nd p
ass
Firs
t pas
s
Third
pas
s
A
A
A
A
Evaporator(EV)
Figure 7 Position of boiler supports and heat exchangers (dimensions are in mm)
will be discretized by a four-node doubly curved thin shellelement using the reduced integrationwith hourglass controlThe finite element has the codename S4R5 and it is applied forsmall deformations and has five degrees of freedom per node
The load of the mass of boiler structure will be taken intoconsideration for the calculation of reactions in the supportsof ldquoMilanordquo steam boiler (Figure 6) Other loads such as themass of working fluid the fouling mass that is depositedon the heating surfaces during the combustion process
the mass of refractory and the mass of insulation will not beconsidered here Pipematerial ofmembranewalls is P235GHmaterial of membrane tape and buckstays is S235JRG2 andmaterial of chambers is 16Mo3 All three steels belong tothe group of low-carbon steels with le 03 carbon Sincethe boiler membrane walls are evaporator heating surfacesthe calculation temperature is 120599 = 275
∘C Assuming thatthe mechanical properties of boiler structure are isotropic[36] the modulus of elasticity for all three materials is
8 The Scientific World Journal
Table 1 List of positions according to Figure 4
Pos Type Dimensions Pos Type Dimensions
1 Shell and end of drum 1206011200 times 35mm 14 Collector header ofside wall 1206011397 times 125mm
2 Downcomers 1206011683 times 16mm 15 Collector header ofrear wall of third pass 1206011397 times 125mm
3 Connecting pipe 120601889 times 88mm 16 Side wall of secondpass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 12
4 Collector header ofrear wall of first pass 1206011397 times 125mm 17 Rear wall of second
pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
5 Front wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
18 Side wall of third pass
Pipe 120601483 times 45mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 15
6 Side wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 21
19 Rear wall of third pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
7 Rear wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
20 Buckstays HE-B120
8 Collector header ofwall of hopper 1206011397 times 125mm 21
Distributor header ofrear wall of second
pass1206011397 times 125mm
9 Connecting pipes 120601483 times 4mm 22 Wall of hopper
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
10 Distributor header ofside wall 1206011683 times 20mm 23 Distributor header of
rear wall of first pass 1206011397 times 125mm
11 Distributor header offront wall 1206011397 times 125mm 24 Distributor header of
wall of hopper 1206011397 times 125mm
12Collector header offront and rear wall of
second pass1206011397 times 125mm 25 Distributor header of
rear wall of third pass 1206011397 times 125mm
13 Side wall in transitionzone
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 34
approximately equal and amounts to 119864 = 18712GPa For thevalue of Poissonrsquos factor ] = 03 is used
Due to the single boiler symmetry for the calculationusing the finite element method it is sufficient to model onlyone-half of the boiler geometry (Figures 4 and 5) The boileris supported by ten supports five on the distributor chamber
of the left side wall and five on the distributor chamber of theright side wall (Figure 7) In the third pass of the boiler theheat exchangers were installed that is one evaporator andthree superheaters The heat exchangers were supported onthe side walls of the third pass Due to the weight of heatexchangers the load of the left and right side wall of the third
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
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DistributedSensor Networks
International Journal of
The Scientific World Journal 3
N12N12N21 N21N1
N1N2 N2
120572212057221205721 1205721
AmAp
Am equivAp
Figure 1 Section forces in the membrane wall that is the equivalent orthotropic plate with the membrane stiffness of membrane wall A119898
equivalent to the membrane stiffness of orthotropic plate A119901
M2
M1M12M21
120572212057221205721 1205721
DmDp
DmequivDp
M2M21 M1
M12
Figure 2 Section moments in the membrane wall that is the equivalent orthotropic plate with the bending stiffness of membrane wallD119898
equivalent to the bending stiffness of orthotropic plateD119901
elasticity matrix for bending loads of equivalent orthotropicplate 120576
1 1205762 and 120576
12are the membrane deformations and 120581
1
1205812 and 120581
12are the curvatures of neutral surface of structurally
orthotropic plate that is the equivalent orthotropic plateThe members of elasticity matrix referring to the mem-
brane stiffness [30 34] of membrane wall can be calculatedusing the following expressions
11986011
=
1198641198981
sdot ℎ
1 minus ]11989812
sdot ]11989821
11986012
=
1198641198982
sdot ℎ sdot ]11989812
1 minus ]11989812
sdot ]11989821
11986022
=
1198641198982
sdot ℎ
1 minus ]11989812
sdot ]11989821
11986033
= 11986611989812
sdot ℎ
(3)
where1198641198981
is modulus of elasticity for themembrane stiffnessin the direction of axis 120572
1(the axis parallel to the axis of
pipe in the membrane wall) 1198641198982
is modulus of elasticity forthe membrane stiffness in the direction of axis 120572
2(the axis
perpendicular to the axis of pipe in themembrane wall) ]11989812
is Poissonrsquos ratio for the membrane stiffness in the directionof axis 120572
1 ]11989821
is Poissonrsquos ratio for the membrane stiffnessin the direction of axis 120572
2 and 119866
11989812is shear modulus for
the membrane stiffness The members of elasticity matrix
referring to the bending stiffness [29 33] of membrane wallcan be calculated using the following expressions
11986311
=
1198641198871
sdot ℎ
3
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986312
=
1198641198872
sdot ℎ
3sdot ]11988712
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986322
=
1198641198872
sdot ℎ
3
12 sdot (1 minus ]11988712
sdot ]11988721
)
11986333
=
11986611988712
sdot ℎ
3
12
(4)
where the elasticity constants for the bending stiffness areindicated by index 119887 The expression for the wall thicknessof equivalent orthotropic plate [30] can be obtained fromthe equality of moment of inertia of the cross-section ofmembrane wall considering the plane perpendicular to thelongitudinal axes of the membrane pipes (Figure 3) and thecross-section of equivalent orthotropic plate Consider
ℎ =radic
3 sdot 120587
16 sdot 119863 sdot 119896
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) +
(119896 minus 119863) sdot 119905
3
119863 sdot 119896
(5)
4 The Scientific World Journal
h
k
120601D times 120575
1205722
1205722
1205723
1205723
t
b2
Membrane wallkmdashstep of pipe in the
Equivalent orthotropic platehmdashwall thickness of the equivalent orthotropic plate
membrane wall
Figure 3 Geometry of cross-section of membrane wall and equivalent orthotropic plate
1
2
3
4
5
6
7
8
9
10
11
25
24
23
22
21
20
19
18
17
16
15
14
13
12
X
Y
Z
Figure 4 Real calculation geometry model
The Scientific World Journal 5
850
2500
2100
1925
1030
1080
4915
1790
890
11701440
X
Y
Z
1980
Figure 5 Calculation geometry model approximated as the equivalent orthotropic plate (dimensions are in mm)
The elasticity constants of equivalent orthotropic platefor the membrane stiffness can be calculated using theanalytical expressions suggested in the paper [31 32] Theseexpressions are obtained by equalizing the deformations ofmembrane wall and equivalent plate (thickness ℎ) with theequivalent membrane load
1198641198981
=
119864
119896 sdot ℎ
[
120587
4
sdot (119863
2minus (119863 minus 2 sdot 120575)
2) + (119896 minus 119863) sdot 119905]
1198641198982
=
119896 sdot 119864
ℎ sdot [3 sdot (119863120575 minus 1)
3sdot (1205878 minus 1120587) + 119887119905]
11986611989812
asymp
radic1198641198981
sdot 1198641198982
2 sdot (1 +radic]11989812
sdot ]11989821
)
]11989821
= ]11989812
sdot
1198641198982
1198641198981
(6)
where119864 is modulus of elasticity and ]11989812
= ] is Poissonrsquos fac-tor for the isotropic material of membrane wall The expres-sions for the elasticity constants of equivalent orthotropicplate and for the bending stiffness of membrane wall areproposed in the paper [31 32] Same as for the membranestiffness these expressions are also obtained by equalizing
6 The Scientific World Journal
Figure 6 3D-disposition of biomass incineration power plant ldquoMilanordquo
the deformations of membrane wall and equivalent plate(thickness ℎ) with the equivalent bending load
1198641198871
=
119864
119896 sdot ℎ
3sdot [
3 sdot 120587
16
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) + (119896 minus 119863) sdot 119905
3]
1198641198872
= 119864 sdot (
119905
ℎ
)
3
sdot
(119899 sdot 119896)
4
sum
119899
119894=1(119894 sdot 119896)
4minus (119894 sdot 119896 minus 119887)
4
11986611988712
asymp
radic1198641198871
sdot 1198641198872
2 sdot (1 +radic]11988712
sdot ]11988721
)
]11988721
= ]11988712
sdot
1198641198872
1198641198871
(7)
where 119899 is number of pipes in the membrane wall and ]11988712
=
] is Poissonrsquos factor for the isotropic material of membranewall After the homogenization of steam boiler membrane
wall the stiffness matrix of shell element can be calculatedaccording to the expression
k = int
119860
B119879DB 119889119860 (8)
where 119860 is surface of shell element and B is operator ofboundary magnitude
3 Calculation of Reactions in the Steam BoilerSupports for a Real Model of MembraneWall Geometry for the MembraneWalls Approximated by the EquivalentOrthotropic Plate and for the Ideal RigidModel of Boiler Geometry
Thefinite element method using Abaqus 69-3 will be appliedfor the calculation of reactions in the supportsThe real geom-etry of membrane walls (Figure 4) and the membrane wallsapproximated as the equivalent orthotropic plate (Figure 5)
The Scientific World Journal 7
360
100
2120
100
2120
100
100
1035118013851315
1 2 3 4 5
1740
Superheater 1
Superheater 2
Superheater 3
(SH 1)
(SH 2)
(SH 3)
Seco
nd p
ass
Firs
t pas
s
Third
pas
s
A
A
A
A
Evaporator(EV)
Figure 7 Position of boiler supports and heat exchangers (dimensions are in mm)
will be discretized by a four-node doubly curved thin shellelement using the reduced integrationwith hourglass controlThe finite element has the codename S4R5 and it is applied forsmall deformations and has five degrees of freedom per node
The load of the mass of boiler structure will be taken intoconsideration for the calculation of reactions in the supportsof ldquoMilanordquo steam boiler (Figure 6) Other loads such as themass of working fluid the fouling mass that is depositedon the heating surfaces during the combustion process
the mass of refractory and the mass of insulation will not beconsidered here Pipematerial ofmembranewalls is P235GHmaterial of membrane tape and buckstays is S235JRG2 andmaterial of chambers is 16Mo3 All three steels belong tothe group of low-carbon steels with le 03 carbon Sincethe boiler membrane walls are evaporator heating surfacesthe calculation temperature is 120599 = 275
∘C Assuming thatthe mechanical properties of boiler structure are isotropic[36] the modulus of elasticity for all three materials is
8 The Scientific World Journal
Table 1 List of positions according to Figure 4
Pos Type Dimensions Pos Type Dimensions
1 Shell and end of drum 1206011200 times 35mm 14 Collector header ofside wall 1206011397 times 125mm
2 Downcomers 1206011683 times 16mm 15 Collector header ofrear wall of third pass 1206011397 times 125mm
3 Connecting pipe 120601889 times 88mm 16 Side wall of secondpass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 12
4 Collector header ofrear wall of first pass 1206011397 times 125mm 17 Rear wall of second
pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
5 Front wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
18 Side wall of third pass
Pipe 120601483 times 45mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 15
6 Side wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 21
19 Rear wall of third pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
7 Rear wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
20 Buckstays HE-B120
8 Collector header ofwall of hopper 1206011397 times 125mm 21
Distributor header ofrear wall of second
pass1206011397 times 125mm
9 Connecting pipes 120601483 times 4mm 22 Wall of hopper
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
10 Distributor header ofside wall 1206011683 times 20mm 23 Distributor header of
rear wall of first pass 1206011397 times 125mm
11 Distributor header offront wall 1206011397 times 125mm 24 Distributor header of
wall of hopper 1206011397 times 125mm
12Collector header offront and rear wall of
second pass1206011397 times 125mm 25 Distributor header of
rear wall of third pass 1206011397 times 125mm
13 Side wall in transitionzone
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 34
approximately equal and amounts to 119864 = 18712GPa For thevalue of Poissonrsquos factor ] = 03 is used
Due to the single boiler symmetry for the calculationusing the finite element method it is sufficient to model onlyone-half of the boiler geometry (Figures 4 and 5) The boileris supported by ten supports five on the distributor chamber
of the left side wall and five on the distributor chamber of theright side wall (Figure 7) In the third pass of the boiler theheat exchangers were installed that is one evaporator andthree superheaters The heat exchangers were supported onthe side walls of the third pass Due to the weight of heatexchangers the load of the left and right side wall of the third
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
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Shock and Vibration
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DistributedSensor Networks
International Journal of
4 The Scientific World Journal
h
k
120601D times 120575
1205722
1205722
1205723
1205723
t
b2
Membrane wallkmdashstep of pipe in the
Equivalent orthotropic platehmdashwall thickness of the equivalent orthotropic plate
membrane wall
Figure 3 Geometry of cross-section of membrane wall and equivalent orthotropic plate
1
2
3
4
5
6
7
8
9
10
11
25
24
23
22
21
20
19
18
17
16
15
14
13
12
X
Y
Z
Figure 4 Real calculation geometry model
The Scientific World Journal 5
850
2500
2100
1925
1030
1080
4915
1790
890
11701440
X
Y
Z
1980
Figure 5 Calculation geometry model approximated as the equivalent orthotropic plate (dimensions are in mm)
The elasticity constants of equivalent orthotropic platefor the membrane stiffness can be calculated using theanalytical expressions suggested in the paper [31 32] Theseexpressions are obtained by equalizing the deformations ofmembrane wall and equivalent plate (thickness ℎ) with theequivalent membrane load
1198641198981
=
119864
119896 sdot ℎ
[
120587
4
sdot (119863
2minus (119863 minus 2 sdot 120575)
2) + (119896 minus 119863) sdot 119905]
1198641198982
=
119896 sdot 119864
ℎ sdot [3 sdot (119863120575 minus 1)
3sdot (1205878 minus 1120587) + 119887119905]
11986611989812
asymp
radic1198641198981
sdot 1198641198982
2 sdot (1 +radic]11989812
sdot ]11989821
)
]11989821
= ]11989812
sdot
1198641198982
1198641198981
(6)
where119864 is modulus of elasticity and ]11989812
= ] is Poissonrsquos fac-tor for the isotropic material of membrane wall The expres-sions for the elasticity constants of equivalent orthotropicplate and for the bending stiffness of membrane wall areproposed in the paper [31 32] Same as for the membranestiffness these expressions are also obtained by equalizing
6 The Scientific World Journal
Figure 6 3D-disposition of biomass incineration power plant ldquoMilanordquo
the deformations of membrane wall and equivalent plate(thickness ℎ) with the equivalent bending load
1198641198871
=
119864
119896 sdot ℎ
3sdot [
3 sdot 120587
16
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) + (119896 minus 119863) sdot 119905
3]
1198641198872
= 119864 sdot (
119905
ℎ
)
3
sdot
(119899 sdot 119896)
4
sum
119899
119894=1(119894 sdot 119896)
4minus (119894 sdot 119896 minus 119887)
4
11986611988712
asymp
radic1198641198871
sdot 1198641198872
2 sdot (1 +radic]11988712
sdot ]11988721
)
]11988721
= ]11988712
sdot
1198641198872
1198641198871
(7)
where 119899 is number of pipes in the membrane wall and ]11988712
=
] is Poissonrsquos factor for the isotropic material of membranewall After the homogenization of steam boiler membrane
wall the stiffness matrix of shell element can be calculatedaccording to the expression
k = int
119860
B119879DB 119889119860 (8)
where 119860 is surface of shell element and B is operator ofboundary magnitude
3 Calculation of Reactions in the Steam BoilerSupports for a Real Model of MembraneWall Geometry for the MembraneWalls Approximated by the EquivalentOrthotropic Plate and for the Ideal RigidModel of Boiler Geometry
Thefinite element method using Abaqus 69-3 will be appliedfor the calculation of reactions in the supportsThe real geom-etry of membrane walls (Figure 4) and the membrane wallsapproximated as the equivalent orthotropic plate (Figure 5)
The Scientific World Journal 7
360
100
2120
100
2120
100
100
1035118013851315
1 2 3 4 5
1740
Superheater 1
Superheater 2
Superheater 3
(SH 1)
(SH 2)
(SH 3)
Seco
nd p
ass
Firs
t pas
s
Third
pas
s
A
A
A
A
Evaporator(EV)
Figure 7 Position of boiler supports and heat exchangers (dimensions are in mm)
will be discretized by a four-node doubly curved thin shellelement using the reduced integrationwith hourglass controlThe finite element has the codename S4R5 and it is applied forsmall deformations and has five degrees of freedom per node
The load of the mass of boiler structure will be taken intoconsideration for the calculation of reactions in the supportsof ldquoMilanordquo steam boiler (Figure 6) Other loads such as themass of working fluid the fouling mass that is depositedon the heating surfaces during the combustion process
the mass of refractory and the mass of insulation will not beconsidered here Pipematerial ofmembranewalls is P235GHmaterial of membrane tape and buckstays is S235JRG2 andmaterial of chambers is 16Mo3 All three steels belong tothe group of low-carbon steels with le 03 carbon Sincethe boiler membrane walls are evaporator heating surfacesthe calculation temperature is 120599 = 275
∘C Assuming thatthe mechanical properties of boiler structure are isotropic[36] the modulus of elasticity for all three materials is
8 The Scientific World Journal
Table 1 List of positions according to Figure 4
Pos Type Dimensions Pos Type Dimensions
1 Shell and end of drum 1206011200 times 35mm 14 Collector header ofside wall 1206011397 times 125mm
2 Downcomers 1206011683 times 16mm 15 Collector header ofrear wall of third pass 1206011397 times 125mm
3 Connecting pipe 120601889 times 88mm 16 Side wall of secondpass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 12
4 Collector header ofrear wall of first pass 1206011397 times 125mm 17 Rear wall of second
pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
5 Front wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
18 Side wall of third pass
Pipe 120601483 times 45mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 15
6 Side wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 21
19 Rear wall of third pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
7 Rear wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
20 Buckstays HE-B120
8 Collector header ofwall of hopper 1206011397 times 125mm 21
Distributor header ofrear wall of second
pass1206011397 times 125mm
9 Connecting pipes 120601483 times 4mm 22 Wall of hopper
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
10 Distributor header ofside wall 1206011683 times 20mm 23 Distributor header of
rear wall of first pass 1206011397 times 125mm
11 Distributor header offront wall 1206011397 times 125mm 24 Distributor header of
wall of hopper 1206011397 times 125mm
12Collector header offront and rear wall of
second pass1206011397 times 125mm 25 Distributor header of
rear wall of third pass 1206011397 times 125mm
13 Side wall in transitionzone
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 34
approximately equal and amounts to 119864 = 18712GPa For thevalue of Poissonrsquos factor ] = 03 is used
Due to the single boiler symmetry for the calculationusing the finite element method it is sufficient to model onlyone-half of the boiler geometry (Figures 4 and 5) The boileris supported by ten supports five on the distributor chamber
of the left side wall and five on the distributor chamber of theright side wall (Figure 7) In the third pass of the boiler theheat exchangers were installed that is one evaporator andthree superheaters The heat exchangers were supported onthe side walls of the third pass Due to the weight of heatexchangers the load of the left and right side wall of the third
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
The Scientific World Journal 5
850
2500
2100
1925
1030
1080
4915
1790
890
11701440
X
Y
Z
1980
Figure 5 Calculation geometry model approximated as the equivalent orthotropic plate (dimensions are in mm)
The elasticity constants of equivalent orthotropic platefor the membrane stiffness can be calculated using theanalytical expressions suggested in the paper [31 32] Theseexpressions are obtained by equalizing the deformations ofmembrane wall and equivalent plate (thickness ℎ) with theequivalent membrane load
1198641198981
=
119864
119896 sdot ℎ
[
120587
4
sdot (119863
2minus (119863 minus 2 sdot 120575)
2) + (119896 minus 119863) sdot 119905]
1198641198982
=
119896 sdot 119864
ℎ sdot [3 sdot (119863120575 minus 1)
3sdot (1205878 minus 1120587) + 119887119905]
11986611989812
asymp
radic1198641198981
sdot 1198641198982
2 sdot (1 +radic]11989812
sdot ]11989821
)
]11989821
= ]11989812
sdot
1198641198982
1198641198981
(6)
where119864 is modulus of elasticity and ]11989812
= ] is Poissonrsquos fac-tor for the isotropic material of membrane wall The expres-sions for the elasticity constants of equivalent orthotropicplate and for the bending stiffness of membrane wall areproposed in the paper [31 32] Same as for the membranestiffness these expressions are also obtained by equalizing
6 The Scientific World Journal
Figure 6 3D-disposition of biomass incineration power plant ldquoMilanordquo
the deformations of membrane wall and equivalent plate(thickness ℎ) with the equivalent bending load
1198641198871
=
119864
119896 sdot ℎ
3sdot [
3 sdot 120587
16
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) + (119896 minus 119863) sdot 119905
3]
1198641198872
= 119864 sdot (
119905
ℎ
)
3
sdot
(119899 sdot 119896)
4
sum
119899
119894=1(119894 sdot 119896)
4minus (119894 sdot 119896 minus 119887)
4
11986611988712
asymp
radic1198641198871
sdot 1198641198872
2 sdot (1 +radic]11988712
sdot ]11988721
)
]11988721
= ]11988712
sdot
1198641198872
1198641198871
(7)
where 119899 is number of pipes in the membrane wall and ]11988712
=
] is Poissonrsquos factor for the isotropic material of membranewall After the homogenization of steam boiler membrane
wall the stiffness matrix of shell element can be calculatedaccording to the expression
k = int
119860
B119879DB 119889119860 (8)
where 119860 is surface of shell element and B is operator ofboundary magnitude
3 Calculation of Reactions in the Steam BoilerSupports for a Real Model of MembraneWall Geometry for the MembraneWalls Approximated by the EquivalentOrthotropic Plate and for the Ideal RigidModel of Boiler Geometry
Thefinite element method using Abaqus 69-3 will be appliedfor the calculation of reactions in the supportsThe real geom-etry of membrane walls (Figure 4) and the membrane wallsapproximated as the equivalent orthotropic plate (Figure 5)
The Scientific World Journal 7
360
100
2120
100
2120
100
100
1035118013851315
1 2 3 4 5
1740
Superheater 1
Superheater 2
Superheater 3
(SH 1)
(SH 2)
(SH 3)
Seco
nd p
ass
Firs
t pas
s
Third
pas
s
A
A
A
A
Evaporator(EV)
Figure 7 Position of boiler supports and heat exchangers (dimensions are in mm)
will be discretized by a four-node doubly curved thin shellelement using the reduced integrationwith hourglass controlThe finite element has the codename S4R5 and it is applied forsmall deformations and has five degrees of freedom per node
The load of the mass of boiler structure will be taken intoconsideration for the calculation of reactions in the supportsof ldquoMilanordquo steam boiler (Figure 6) Other loads such as themass of working fluid the fouling mass that is depositedon the heating surfaces during the combustion process
the mass of refractory and the mass of insulation will not beconsidered here Pipematerial ofmembranewalls is P235GHmaterial of membrane tape and buckstays is S235JRG2 andmaterial of chambers is 16Mo3 All three steels belong tothe group of low-carbon steels with le 03 carbon Sincethe boiler membrane walls are evaporator heating surfacesthe calculation temperature is 120599 = 275
∘C Assuming thatthe mechanical properties of boiler structure are isotropic[36] the modulus of elasticity for all three materials is
8 The Scientific World Journal
Table 1 List of positions according to Figure 4
Pos Type Dimensions Pos Type Dimensions
1 Shell and end of drum 1206011200 times 35mm 14 Collector header ofside wall 1206011397 times 125mm
2 Downcomers 1206011683 times 16mm 15 Collector header ofrear wall of third pass 1206011397 times 125mm
3 Connecting pipe 120601889 times 88mm 16 Side wall of secondpass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 12
4 Collector header ofrear wall of first pass 1206011397 times 125mm 17 Rear wall of second
pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
5 Front wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
18 Side wall of third pass
Pipe 120601483 times 45mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 15
6 Side wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 21
19 Rear wall of third pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
7 Rear wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
20 Buckstays HE-B120
8 Collector header ofwall of hopper 1206011397 times 125mm 21
Distributor header ofrear wall of second
pass1206011397 times 125mm
9 Connecting pipes 120601483 times 4mm 22 Wall of hopper
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
10 Distributor header ofside wall 1206011683 times 20mm 23 Distributor header of
rear wall of first pass 1206011397 times 125mm
11 Distributor header offront wall 1206011397 times 125mm 24 Distributor header of
wall of hopper 1206011397 times 125mm
12Collector header offront and rear wall of
second pass1206011397 times 125mm 25 Distributor header of
rear wall of third pass 1206011397 times 125mm
13 Side wall in transitionzone
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 34
approximately equal and amounts to 119864 = 18712GPa For thevalue of Poissonrsquos factor ] = 03 is used
Due to the single boiler symmetry for the calculationusing the finite element method it is sufficient to model onlyone-half of the boiler geometry (Figures 4 and 5) The boileris supported by ten supports five on the distributor chamber
of the left side wall and five on the distributor chamber of theright side wall (Figure 7) In the third pass of the boiler theheat exchangers were installed that is one evaporator andthree superheaters The heat exchangers were supported onthe side walls of the third pass Due to the weight of heatexchangers the load of the left and right side wall of the third
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
6 The Scientific World Journal
Figure 6 3D-disposition of biomass incineration power plant ldquoMilanordquo
the deformations of membrane wall and equivalent plate(thickness ℎ) with the equivalent bending load
1198641198871
=
119864
119896 sdot ℎ
3sdot [
3 sdot 120587
16
sdot (119863
4minus (119863 minus 2 sdot 120575)
4) + (119896 minus 119863) sdot 119905
3]
1198641198872
= 119864 sdot (
119905
ℎ
)
3
sdot
(119899 sdot 119896)
4
sum
119899
119894=1(119894 sdot 119896)
4minus (119894 sdot 119896 minus 119887)
4
11986611988712
asymp
radic1198641198871
sdot 1198641198872
2 sdot (1 +radic]11988712
sdot ]11988721
)
]11988721
= ]11988712
sdot
1198641198872
1198641198871
(7)
where 119899 is number of pipes in the membrane wall and ]11988712
=
] is Poissonrsquos factor for the isotropic material of membranewall After the homogenization of steam boiler membrane
wall the stiffness matrix of shell element can be calculatedaccording to the expression
k = int
119860
B119879DB 119889119860 (8)
where 119860 is surface of shell element and B is operator ofboundary magnitude
3 Calculation of Reactions in the Steam BoilerSupports for a Real Model of MembraneWall Geometry for the MembraneWalls Approximated by the EquivalentOrthotropic Plate and for the Ideal RigidModel of Boiler Geometry
Thefinite element method using Abaqus 69-3 will be appliedfor the calculation of reactions in the supportsThe real geom-etry of membrane walls (Figure 4) and the membrane wallsapproximated as the equivalent orthotropic plate (Figure 5)
The Scientific World Journal 7
360
100
2120
100
2120
100
100
1035118013851315
1 2 3 4 5
1740
Superheater 1
Superheater 2
Superheater 3
(SH 1)
(SH 2)
(SH 3)
Seco
nd p
ass
Firs
t pas
s
Third
pas
s
A
A
A
A
Evaporator(EV)
Figure 7 Position of boiler supports and heat exchangers (dimensions are in mm)
will be discretized by a four-node doubly curved thin shellelement using the reduced integrationwith hourglass controlThe finite element has the codename S4R5 and it is applied forsmall deformations and has five degrees of freedom per node
The load of the mass of boiler structure will be taken intoconsideration for the calculation of reactions in the supportsof ldquoMilanordquo steam boiler (Figure 6) Other loads such as themass of working fluid the fouling mass that is depositedon the heating surfaces during the combustion process
the mass of refractory and the mass of insulation will not beconsidered here Pipematerial ofmembranewalls is P235GHmaterial of membrane tape and buckstays is S235JRG2 andmaterial of chambers is 16Mo3 All three steels belong tothe group of low-carbon steels with le 03 carbon Sincethe boiler membrane walls are evaporator heating surfacesthe calculation temperature is 120599 = 275
∘C Assuming thatthe mechanical properties of boiler structure are isotropic[36] the modulus of elasticity for all three materials is
8 The Scientific World Journal
Table 1 List of positions according to Figure 4
Pos Type Dimensions Pos Type Dimensions
1 Shell and end of drum 1206011200 times 35mm 14 Collector header ofside wall 1206011397 times 125mm
2 Downcomers 1206011683 times 16mm 15 Collector header ofrear wall of third pass 1206011397 times 125mm
3 Connecting pipe 120601889 times 88mm 16 Side wall of secondpass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 12
4 Collector header ofrear wall of first pass 1206011397 times 125mm 17 Rear wall of second
pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
5 Front wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
18 Side wall of third pass
Pipe 120601483 times 45mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 15
6 Side wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 21
19 Rear wall of third pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
7 Rear wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
20 Buckstays HE-B120
8 Collector header ofwall of hopper 1206011397 times 125mm 21
Distributor header ofrear wall of second
pass1206011397 times 125mm
9 Connecting pipes 120601483 times 4mm 22 Wall of hopper
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
10 Distributor header ofside wall 1206011683 times 20mm 23 Distributor header of
rear wall of first pass 1206011397 times 125mm
11 Distributor header offront wall 1206011397 times 125mm 24 Distributor header of
wall of hopper 1206011397 times 125mm
12Collector header offront and rear wall of
second pass1206011397 times 125mm 25 Distributor header of
rear wall of third pass 1206011397 times 125mm
13 Side wall in transitionzone
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 34
approximately equal and amounts to 119864 = 18712GPa For thevalue of Poissonrsquos factor ] = 03 is used
Due to the single boiler symmetry for the calculationusing the finite element method it is sufficient to model onlyone-half of the boiler geometry (Figures 4 and 5) The boileris supported by ten supports five on the distributor chamber
of the left side wall and five on the distributor chamber of theright side wall (Figure 7) In the third pass of the boiler theheat exchangers were installed that is one evaporator andthree superheaters The heat exchangers were supported onthe side walls of the third pass Due to the weight of heatexchangers the load of the left and right side wall of the third
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
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VLSI Design
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Shock and Vibration
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Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
The Scientific World Journal 7
360
100
2120
100
2120
100
100
1035118013851315
1 2 3 4 5
1740
Superheater 1
Superheater 2
Superheater 3
(SH 1)
(SH 2)
(SH 3)
Seco
nd p
ass
Firs
t pas
s
Third
pas
s
A
A
A
A
Evaporator(EV)
Figure 7 Position of boiler supports and heat exchangers (dimensions are in mm)
will be discretized by a four-node doubly curved thin shellelement using the reduced integrationwith hourglass controlThe finite element has the codename S4R5 and it is applied forsmall deformations and has five degrees of freedom per node
The load of the mass of boiler structure will be taken intoconsideration for the calculation of reactions in the supportsof ldquoMilanordquo steam boiler (Figure 6) Other loads such as themass of working fluid the fouling mass that is depositedon the heating surfaces during the combustion process
the mass of refractory and the mass of insulation will not beconsidered here Pipematerial ofmembranewalls is P235GHmaterial of membrane tape and buckstays is S235JRG2 andmaterial of chambers is 16Mo3 All three steels belong tothe group of low-carbon steels with le 03 carbon Sincethe boiler membrane walls are evaporator heating surfacesthe calculation temperature is 120599 = 275
∘C Assuming thatthe mechanical properties of boiler structure are isotropic[36] the modulus of elasticity for all three materials is
8 The Scientific World Journal
Table 1 List of positions according to Figure 4
Pos Type Dimensions Pos Type Dimensions
1 Shell and end of drum 1206011200 times 35mm 14 Collector header ofside wall 1206011397 times 125mm
2 Downcomers 1206011683 times 16mm 15 Collector header ofrear wall of third pass 1206011397 times 125mm
3 Connecting pipe 120601889 times 88mm 16 Side wall of secondpass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 12
4 Collector header ofrear wall of first pass 1206011397 times 125mm 17 Rear wall of second
pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
5 Front wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
18 Side wall of third pass
Pipe 120601483 times 45mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 15
6 Side wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 21
19 Rear wall of third pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
7 Rear wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
20 Buckstays HE-B120
8 Collector header ofwall of hopper 1206011397 times 125mm 21
Distributor header ofrear wall of second
pass1206011397 times 125mm
9 Connecting pipes 120601483 times 4mm 22 Wall of hopper
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
10 Distributor header ofside wall 1206011683 times 20mm 23 Distributor header of
rear wall of first pass 1206011397 times 125mm
11 Distributor header offront wall 1206011397 times 125mm 24 Distributor header of
wall of hopper 1206011397 times 125mm
12Collector header offront and rear wall of
second pass1206011397 times 125mm 25 Distributor header of
rear wall of third pass 1206011397 times 125mm
13 Side wall in transitionzone
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 34
approximately equal and amounts to 119864 = 18712GPa For thevalue of Poissonrsquos factor ] = 03 is used
Due to the single boiler symmetry for the calculationusing the finite element method it is sufficient to model onlyone-half of the boiler geometry (Figures 4 and 5) The boileris supported by ten supports five on the distributor chamber
of the left side wall and five on the distributor chamber of theright side wall (Figure 7) In the third pass of the boiler theheat exchangers were installed that is one evaporator andthree superheaters The heat exchangers were supported onthe side walls of the third pass Due to the weight of heatexchangers the load of the left and right side wall of the third
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
International Journal of
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Shock and Vibration
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International Journal of
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DistributedSensor Networks
International Journal of
8 The Scientific World Journal
Table 1 List of positions according to Figure 4
Pos Type Dimensions Pos Type Dimensions
1 Shell and end of drum 1206011200 times 35mm 14 Collector header ofside wall 1206011397 times 125mm
2 Downcomers 1206011683 times 16mm 15 Collector header ofrear wall of third pass 1206011397 times 125mm
3 Connecting pipe 120601889 times 88mm 16 Side wall of secondpass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 12
4 Collector header ofrear wall of first pass 1206011397 times 125mm 17 Rear wall of second
pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
5 Front wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
18 Side wall of third pass
Pipe 120601483 times 45mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 15
6 Side wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 21
19 Rear wall of third pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
7 Rear wall of first pass
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
20 Buckstays HE-B120
8 Collector header ofwall of hopper 1206011397 times 125mm 21
Distributor header ofrear wall of second
pass1206011397 times 125mm
9 Connecting pipes 120601483 times 4mm 22 Wall of hopper
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 23
10 Distributor header ofside wall 1206011683 times 20mm 23 Distributor header of
rear wall of first pass 1206011397 times 125mm
11 Distributor header offront wall 1206011397 times 125mm 24 Distributor header of
wall of hopper 1206011397 times 125mm
12Collector header offront and rear wall of
second pass1206011397 times 125mm 25 Distributor header of
rear wall of third pass 1206011397 times 125mm
13 Side wall in transitionzone
Pipe 12060157 times 4mmTape 119905 = 6mmStep 119896 = 90mmNumber of pipes
119899 = 34
approximately equal and amounts to 119864 = 18712GPa For thevalue of Poissonrsquos factor ] = 03 is used
Due to the single boiler symmetry for the calculationusing the finite element method it is sufficient to model onlyone-half of the boiler geometry (Figures 4 and 5) The boileris supported by ten supports five on the distributor chamber
of the left side wall and five on the distributor chamber of theright side wall (Figure 7) In the third pass of the boiler theheat exchangers were installed that is one evaporator andthree superheaters The heat exchangers were supported onthe side walls of the third pass Due to the weight of heatexchangers the load of the left and right side wall of the third
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
The Scientific World Journal 9
Table 2 Masses of constituent structural elements for half geometry of ldquoMilanordquo boiler
Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg Pos Mass kg1 1967 7 639 13 315 19 786 25 432 595 8 43 14 197 20 668 SH1 11853 23 9 17 15 43 21 43 SH2 11854 43 10 402 16 702 22 157 SH3 5275 893 11 43 17 721 23 43 EV 536 1184 12 43 18 1018 24 43
Table 3 Elasticity constants and wall thickness of equivalent orthotropic plate for membrane walls of ldquoMilanordquo boiler
Membrane wall(position)
ℎmm
1198641198981
GPa
1198641198982
GPa
11986611989812
GPa ]
11989821
1198641198871
GPa1198641198872
GPa11986611988712
GPa ]
11988721
5 7 17 19 22 2348 76492 1367 4915 0005361 454159 8064 29095 00053276 2348 76492 1367 4915 0005361 454159 8023 29025 000530013 2348 76492 1367 4915 0005361 454159 8203 29336 000541916 2348 76492 1367 4915 0005361 454159 7690 28439 000508018 2040 88592 3880 8722 0013138 442956 9583 31199 0006490
Detail A
A
X
Y
Z
Figure 8 Finite element mesh-calculation model APPROX
pass is identical For the calculation of reactions in the boilersupports half of the weight of individual heat exchanger willbe used as the equivalent tangential surface pressure on theside wall of the third pass This pressure is applied on surface
Table 4 Members of elasticity matrix of equivalent orthotropicplate for membrane walls of ldquoMilanordquo boiler for membrane stiffness
Membrane wall(position)
11986011
Nmm11986012
Nmm11986022
Nmm11986033
Nmm5 6 7 13 16 1719 22 1799282 9646 32152 115438
18 1814749 23843 79476 177966
Table 5Members of elasticitymatrix of equivalent orthotropic platefor membrane walls of ldquoMilanordquo boiler for bending stiffness
Membrane wall(position)
11986311
Nsdotmm11986312
Nsdotmm11986322
Nsdotmm11986333
Nsdotmm5 7 17 19 22 491000497 2615341 8717804 314048896 490996567 2602240 8674134 3132927213 491014120 2660750 8869166 3166540416 490964096 2494004 8313348 3069652418 314156438 2038906 6796354 22084218
Table 6 Reactions in the boiler supports for the influence of totalmass
Reactions inboiler supports 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 22748 27020 32657 38515 12676APPROX 24183 25992 31015 40026 12499RIGID 27234 22608 31088 36609 16077Δ119860 631 minus380 minus503 392 minus140
Δ119870 1972 minus1633 minus480 minus495 2683
A of membrane wall on which the carriers of heat exchangersare welded (Figure 7) Bending of the side membrane wallsof the third pass due to the load of heat exchangers was nottaken into consideration
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
10 The Scientific World Journal
Table 7 Reactions in the boiler supports for the influence of mass of boiler without the mass of heat exchangers
Reactions in boiler supportswithout the mass of heat exchangers 119865
1198771 N 119865
1198772 N 119865
1198773 N 119865
1198774 N 119865
1198775 N
REAL 24329 29007 24633 21190 5521APPROX 25790 27681 23752 21822 5574RIGID 27397 21905 34552 10957 9869Δ119860 601 minus457 minus358 298 096
Δ119870 1261 minus2448 4027 minus4829 7875
B
Detail B
X
Y
Z
Figure 9 Finite element mesh-calculation model REAL
The masses of individual structural elements of boilermarked according to Figures 4 and 7 and Table 1 are givenin Table 2 The inhomogeneity of material of boiler structurewill not be taken into consideration here It is assumed thatthe geometry of boiler is ideal without the tolerances ofproduction and assembly as well as the tolerances of semifin-ished rolled products built into the boiler It is assumed thatthe mechanical properties of material of boiler structure areisotropic that is that anisotropy of the welded joints andsemifinished rolled products does not influence significantlythe reactions in the boiler supports
The mass of half of boiler without the heat exchangersis 119898
1015840= 10671 kg and with the heat exchangers it is 119898 =
13621 kg The membrane walls of ldquoMilanordquo boiler are made
with the step of 90mm Two dimensions of the cross-sectionof pipe (12060157 times 4mm and 120601483 times 45mm) are appliedas well as the membrane tape (thickness 6mm) For theboiler membrane walls it is possible to calculate the elasticityconstants of equivalent orthotropic plate (Table 3) accordingto expressions (2) and (7) The members of elasticity matrix(Tables 4 and 5) which will be applied to the finite element ofequivalent orthotropic plate will be calculated according toexpressions (3) and (4)
In this paper the results of six different calculationsof reactions in the supports of ldquoMilanordquo boiler will bepresented the calculation of real geometry of boiler (REAL)discretized by the shell finite element the calculation withthe approximation of membrane walls as the plateshell ofequivalent stiffness (APPROX) and the calculationwhere theboiler is considered as a rigid body (RIGID) Each calculationis made with the load of the mass of boiler with and withoutthe mass of heat exchangers
The calculation model for the real geometry of boilerconsisted of 18943590 variables that include the degrees offreedom and Lagrange multipliers and for the approximatedgeometry of boilermembranewalls as the plateshell of equiv-alent stiffness the calculation model consisted of 1619526variables (degrees of freedom and Lagrange multipliers) Inboth cases 4-node finite element S4R5 was predominantlyused and an extremely triangular element was created by thecollapse of one node of 4-node element S4R5 (Figures 8 and9)
The reaction forces in the supports for the influence oftotal mass of boiler are given in Table 6 and the reactionforces for the influence of mass of boiler without the massof heat exchangers are given in Table 7 The reaction forcesin the boiler supports are denoted according to Figure 7In Tables 6 and 7 the deviations of reaction forces forcalculation APPROX (compared to calculation REAL) werecalculated and the deviation was expressed as a percentageand marked as Δ
119860 In the same way the deviation of reaction
forces for calculation RIGID (compared to calculation REAL)was calculated and it was expressed as a percentage andmarked as Δ
119870 The deviations were calculated according to
the following expressions
Δ119860
= (
119865Ri (APPROX)
119865Ri (REAL)minus 1) sdot 100
Δ119870
= (
119865Ri (RIGID)
119865Ri (REAL)minus 1) sdot 100
(9)
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
The Scientific World Journal 11
4 Conclusion
The investigation of the influence of approximation of steamboilermembranewalls using the equivalent orthotropic platefor the calculation of reactions in the boiler supports ispresented in this paper The expressions for the elasticityconstants that have been published in previous papers [30ndash32] were applied
(i) The reactions in the boiler supports were calculatedwith the assumption that the structure of boiler isideally rigid
(ii) The calculations were carried out for the load of themass of boiler with and without the mass of heatexchangers in the third pass of boiler
(iii) The number of variables for the calculation modelREAL was more than 11 times higher than for thecalculation model APPROX Therefore the calcula-tion of node values of model REAL lasted for 1 h23min and 50 s and for the model APPROX 1minand 56 sThe calculation was carried out on a PCwithCPU Intel(R) Core (TM) i7 24GB RAM and 64-bitoperating system
(iv) The deviations of results for the reactions in thesupports for the calculation APPROX compared tothe calculation REAL are max 631 for the load ofthe total mass of boiler and 601 for the load withoutthe mass of heat exchangers
(v) The deviations of results for the calculation RIGIDcompared to the calculation REAL are 7875 for theload without the mass of heat exchangers
(vi) If the results of calculation REAL are accepted asapproximately accurate then it can be concludedthat the application of calculation model APPROX isacceptable for practical use Due to the huge errorthe calculationmodel RIGID is not recommended forpractical use
(vii) Using themethod of equivalent stiffness ofmembranewall more accurate results of calculation could beacquired if when calculating themodulus of elasticity1198641198872 the membrane pipe would be observed as a solid
body and not as an ideal rigid body [32]
(viii) Additional improvements could be achieved by tak-ing into consideration the transverse shear stiffness
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgment
The authors would like to thank PLANUM doo fromSlavonski Brod in Croatia for usage of technical data whichwere needed for this research
References
[1] V Milosevic-Mitic B Gacesa N Anđelic and T ManeskildquoNumerical calculation of the water-tube boiler using finiteelement of the orthotropic platerdquo Structural Integrity and Lifevol 12 no 3 pp 185ndash190 2012
[2] M T Huber ldquoDie grundlagen einer rationellen berechnungder kreuzweise bewehrten eisenbetonplattenrdquo Zeitschrift desOsterreichischen Ingenieur- und Architekten-Vereins vol 66 pp557ndash564 1914
[3] M T Huber ldquoDie Theorie der kreuzweise bewehrtenEisenbeton-platten nebst Anwendungen auf mehrerebautechnisch wichtige Aufgaben uber rechteckige PlattenrdquoBauingenieur vol 4 pp 354ndash360 1923
[4] M T Huber Probleme der Statik Technisch WichtigerOrthotroper Platten Nakkadem Akadenji Nauk TechnicznychWarszawa Poland 1929
[5] W Flugge ldquoDie Stabilitat der Kreiszylinderschalerdquo Ingenieur-Archiv vol 3 no 5 pp 463ndash506 1932
[6] A van der Neut ldquoThe general instability of stiffened cylindricalshells under axial compressionrdquo Report S 314 National Lucht-vaartlaboratorium 1947
[7] F A Dale R C T Smith et al ldquoGrid sandwich panels in com-pressionrdquo Report ACA-16 Australian Council for Aeronautics1945
[8] C B Smith T B Heebink and C B Norris ldquoThe effective stiff-ness of a stiffener attached to a flat plywood platerdquo Report 1557U S Department of Agriculture Forest Products Laboratory1946
[9] A Pfluger ldquoZumBeulproblem der anisotropen RechteckplatterdquoIngenieur-Archiv vol 16 no 2 pp 111ndash120 1947
[10] A Gomza and P Seide ldquoMinimum-weight design of simplysupported transversely stiffened plates under compressionrdquoNACA TN 1710 1948
[11] C Libove and R E Hubka ldquoElastic constants for corrugated-core sandwich platesrdquo NACA TN 2289 1951
[12] C Libove and S B Batdorf ldquoA general small-deflection theoryfor flat sandwich platesrdquo NACA Report 899 1948
[13] E Reissner ldquoOn small bending and stretching of sandwich-typeshellsrdquo International Journal of Solids and Structures vol 13 no12 pp 1293ndash1300 1977
[14] M Stein and J Mayers ldquoA small-deflection theory for curvedsandwich platesrdquo NACA Report 1008 1951
[15] N J Huffington Jr ldquoTheoretical determination of rigidityproperties of orthogonally stiffened platesrdquo Journal of AppliedMechanics vol 23 pp 15ndash20 1956
[16] G Gerard ldquoMinimum weight analysis of orthotropic platesunder compressive loadingrdquo Journal of the Aeronautical Sci-ences vol 27 no 1 pp 21ndash26 1960
[17] M Baruch and J Singer ldquoEffect of eccentricity of stiffenerson the general instability of stiffened cylindrical shells underhydrostatic pressurerdquo Journal ofMechanical Engineering Sciencevol 5 no 1 pp 23ndash27 1963
[18] R J Clifton J C L Chang and T Au ldquoAnalysis of orthotropicplate bridgesrdquo ASCE Journal of the Structural Division vol 89no 5 pp 133ndash171 1963
[19] W J Stroud ldquoElastic constants for bending and twisting ofcorrugation-stiffened panelsrdquo NASA TR R 166 1963
[20] R R Meyer and R J Bellefante ldquoFabrication and experimentalevaluation of common domes having waffle-like stiffeningmdashpart Imdashprogram developmentrdquo Report SM 47742 DouglasMissile amp Space Systems Division 1964
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
12 The Scientific World Journal
[21] T-C Soong ldquoBuckling of cylindrical shells with eccentricspiral-type stiffenersrdquo AIAA Journal vol 7 no 10 pp 65ndash721969
[22] R R Meyer ldquoComments on buckling of cylindrical shells witheccentric spiral-type stiffenersrdquo AIAA Journal vol 7 no 10 p2047 1969
[23] T-C Soong ldquoReply by author to R R Meyerrdquo AIAA Journalvol 7 no 10 pp 2047ndash2048 1969
[24] F Nishino R P Pama and S-L Lee ldquoOrthotropic plateswith eccentric stiffenersrdquo International Association of BridgeStructural Engineering vol 34 no 2 pp 117ndash129 1974
[25] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo in Proceedingsof the AIAAASMEAHS 20th Structures Structural Dynamicsand Materials Conference AIAA paper 79-0756 1979
[26] W L Ko ldquoElastic constants for superplasticallyformeddiffusion-bonded sandwich structuresrdquo AIAA Journalvol 18 no 8 pp 986ndash987 1980
[27] W L Ko ldquoElastic stability of superplastically formeddiffusion-bonded orthogonally corrugated core sandwich platesrdquo inProceedings of the AIAAASMEAHS 21st Structures StructuralDynamics and Materials Conference AIAA paper 80-06831980
[28] N Jaunky N F Knight Jr and D R Ambur ldquoFormulation ofan improved smeared stiffener theory for buckling analysis ofgrid-stiffened composite panelsrdquo NASA TM 110162 1995
[29] N Jaunky F Knight and D R Ambur ldquoFormulation of animproved smeared stiffener theory for buckling analysis of grid-stiffened composite panelsrdquo Composites B vol 27 pp 519ndash5261996
[30] J Sertic D Kozak D Damjanovic and P Konjatic ldquoHomoge-nization of steam boiler membrane wallrdquo in Proceedings of 7thInternational Congress of Croatian Society of Mechanics Zadar2012
[31] J Sertic I Gelo D Kozak D Damjanovic and P KonjeticldquoTeoretical determination of elasticity constants for steamboiler membrane wall as the structurally ortotropic platerdquo inProceeding of 4th International Scientific and Expert Conferenceof the International TEAM Society Slavonski Brod 2012
[32] J Sertic I Gelo D Kozak D Damjanovic and P KonjaticldquoTheoretical determination of elasticity constants for steamboiler membrane wall as the structurally orthotropic platerdquoTechnical Gazette vol 20 no 4 pp 697ndash703 2013
[33] R Solecki and R J Conant Advanced Mechanics of MaterialsOxford University Press Oxford UK 2003
[34] E Ventsel and T Krauthammer Thin Plates and Shells TheoryAnalysis and Applications Marcel Dekker Basel Switzerland2001
[35] V V Novozhilov Thin Shell Theory Noordhoff GroningenGermany 1964
[36] ASME B311 1995
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of