Structural Engineering Imperfections
Transcript of Structural Engineering Imperfections
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Im erfections
Introduction into analysis
global sway imperfections
bracing system imperfections Example Portal frame
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Geometrical Im erfections
Variance of dimensions of a structure or a memberb
flatness of a member
e0
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Geometrical Im erfections
N
L eo,d
Frame imperfection Member Imperfection
Frame imperfection always to be allowed for
Member imperfection: only for slender members (rare)
,
covered in the relevant buckling
curves
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Material & Structural Im erfections
Residual stresses: fy
Distribution in a I-section rr
Apply load eccentricities in joints of the structure
e0
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In order to cover the effects of imperfections, engineers
need to make appropriate allowances in the structural
analysis.
The following imperfections should be taken into account:
Cover lack of verticality for frames or straightness
of structure restrained b bracin s
Local imperfections for individual members
Cover lack of straightness or flatness of a memberand residual stresses of the member
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rame mper ec on can
be replaced by an
e uivalent closed s stem
F1
of horizontal forcesapplied at the floor levels
F2nc u ng e oun a on
level).F2
h
For building frames sway
imperfections, ,
may be disregardedwhere:
(F1+F2)/2 (F1+F2)/2
Equivalent forcesEdEd V15.0
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The factor can be calculated from equation (5.5) of EN 1993:
mh
0=
Where, 0 is the basic value:h is the reduction factor for height h applicable to columns:
13
2but
2=
hh
h
is the height of the structure in meters
m is the reduction factor for the number of columns in a row:
+= mm 15.0
s e num er o co umns n a row
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equivalent closed system of horizontal forces, introduced
for each column.
EdEd
L
eNEd 04
2
08
L
eNEd0e
eNEd 04
NEd NEd
L
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of members for flexural buckling e0/Lare given in Table
5.1 in EN 1993.
ere, s e mem er eng
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Usuall local im erfections are i nored in lobal
analysis and covered by reduction factors and LT in
member checks.
for the frame is sensitive to 2nd order effects, local bow
im erfections should be incor orated into structural
analysis when:
A member has at least one moment resistant end joint;
The slenderness
Ed
y
N
f5.0>
W ere, NEd s t e es gn va ue o t e compress on orce
is the slenderness for the member considered as .
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Bracing systems may provide lateral stability of a strut in
compression or a beam in bending
For members to be restrained, the strut/beam should beconsidered with a geometrical imperfection (initial bow)
an initial bow imperfection.
=
Where, Lis the span of the bracing system
0 m
+= mm 115.0
In which m is the number of members to be restrained
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The bow with amplitudee0 may be replaced by transverse
uniform loadingqd
he loading qd corresponds to impact of sum of theamplitude e0 and the in-plane deflection of the bracing
q.
e0NEd NEdMember in
q08e
Nq
compression
(or compression
flan e force
of a beam)
L
Bracing
system
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-
he members of the ortal frame are ro osed as made of
rolled rods (beam: 533210 UB109, column: 305305
UC158).
hr=2000
=
L=24000
Figure 1
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The combinations of loads are anal zed refer to Fi ure 2:
self-weight & imposed load and wind load
w = 10kN/m
40kN40kNim 1
Figure 2
+3kN/m -2kN/m
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For formulas see EN 1993-1-1
( ) kNVkNHEdEd
4880241015.015.04085 =+=
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Global imperfections:
kN96.0)802410(003.01imp =+== V
Internal forces (loading + imperfections):
NEd (kN) VEd (kN) MEd (kNm)
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Local imperfections for global analysis only if simultaneously
(column concerned):
One end of the member features a rigid connection: OK
Slenderness for systemic length is greater than:
8.21024.168
5,05,03
Ed
y =
=>N
In this case,
8000crh
(this condition is not met)8.256.094.09.939.931
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Structural behaviour
Types of structural analysis
2nd order analysis
Elastic global analysis
as c g o a ana ys s
Simple modelling of structural analysis
Example - 2nd order effects in portal frame
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Structural Modelin for Anal sis
BeamsJoint
-
Joints
Beam-column
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Framing and joints
Continuous framing: rigid joint
Semi-continuous framing: semi-rigid joint
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Load
Load parameter
Peak load
Frame Elastic limit
Displacement parameter
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c ua response o e rame s non near
Linear behaviour limited
Non-linear behaviour due to:
(second order effects)
Material yielding
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Sway
Load
D sp acement
HEdHEd
NEd NEd
xx
h
FrameM(x) = HEdxM(h) = HEdh
M(x) = HEdx + p + P (x/h)M(x) = HEdh + P
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P- effect :
due to floor swa
1st order frame stiffness modified
dominant effect
P- effect : due to beam-column deflection
1st order member stiffness modified
significant only for relatively slender members which is
rare
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Aims of global frame analysis
Determine the corresponding deformations
Means Adequate models incorporating assumptions about the
behaviour of the structure and its com onent:
members and joints
Basic principles to be satisfied:
Equilibrium throughout the structure
ompa y o e orma on e ween e rame componen s
Constitutive lawsfor the frame components
Frame model - element model
must satisfy the basic principles
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T f St t l A l i
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Type of Structural Analysis
The internal forces & moments may be determined usinge er:
First order analysis:
,
Second-order analysis:
deformation of the structure, e.g. both the sway
effect (P- effect) and the P- effect (memberdeflection effect).
he second-order effects should be considered if they
increase the action effects significantly or modify.
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Elastic global analysis should be based on the
assumption that the stress-strain behaviour is linear,
.
,
if the resistance of the section is based on its plastic
resistance.
Elastic global analysis may also be used for cross
sec ons e res s ance o w c are m e y oca
buckling.
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Elastic Global Analysis
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Elastic Global Analysis
General types of Elastic analysis:
LA: Linear elastic analysis;
LBA: Linear bifurcation anal sis
GNA: Geometrically non-linear analysis;GNIA: Geometrically non-linear with imperfections analysis.
Simplified scheme of elastic analyses:
LBAFcr
e
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Method of Structural Analysis
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Method of Structural Analysis
1st order elastic analysis Indefinite linear elastic response of member sections and of
joints
configuration
MElastic
ElasticMj
Mj
MM
Moment rotation characteristic of the section Moment rotation characteristic of the joint
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Method of Structural Analysis
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Method of Structural Analysis
Load parameter 2n order elastic analysis
cr
-
elastic response ofmember sections ando n s
Equilibrium
deformedstructure
-
n or er e as c ana ys s
and, if necessary, forP- effect
Displacement parameter
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Plastic lobal anal sis ma be used where:
the members are capable of sufficient rotation capacity to
enable the re uired redistributions of bendin moments to
develop.
the stability of members at plastic hinges can be assured.
Rigid plastic analysis may be applied if no effects of the
deformed geometry have to be considered.
Frigid-plastic analysis
non-linear plasticelastic-plastic analysisplastic hinge
Simplified scheme of
plastic analyses
fibre plasticity
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Method of Structural Analysis
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Method of Structural Analysis Rigid-plastic global analysis
Rigid-plastic member section behaviour
Rigid plastic Rigid plastic
Rigid-plastic joint behaviour when plastic hinges are allowedthere
M
Mpl.Rd Mpl.Rd
Mj,Rd p
M l.Rd
p j
Plastic hingeM
j,RdPlastic hinge
Moment rotation characteristics of the member Moment rotation characteristics of the joint
p p
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Method of Structural Analysis
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Method of Structural AnalysisLoad parameter
1-
Plastic mechanism
3
2
Critical collapse load
LRP3
analysis
W
H
B D B D
h
H
W
w
Easy application for
sim le frames e. .
Beam mechanism
1
Swa mechanism
2
A
C
E A E
industrial portal frames
Serviceabilit deflection
W
H
BD
h
w
check
3
plastic hinge location
A
C
E
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Method of Structural Analysis
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Method of Structural Analysis
Elastic-perfectly plastic global analysis
nd
Deterioration of frame stability as plastic hinges form
M Mj.Rdj
M
M Mpl.Rd
Plastic hinge.
Plastic hingepl.Rd
Elastic-perfectly plastic response of
member sections
Elastic-perfectly plastic response of
joints
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Simple Modeling of Structures
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Simple Modeling of Structures
First-order analysis may be used, if the following criterion issatisfied:
For elastic analysis: 10=Ed
crcr
F
F
.
For plastic analysis: 15=Ed
crcr
F
F
Where,
or using Eq. 5.2 in EN 1993-1-1.
cr
is the design loading on the structure
is the elastic critical buckling load for global instability
Ed
crF
mode based on initial elastic stiffnesses.
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Simple Modeling of structures
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Simple Modeling of structures
A approximative formula for cr given by Clause 5.2.1(4)
Portals with shallow roof slopes;
Beam and column frames
(5.2)EdH,
VEd
Ed
cr=
,
HEd is the horizontal reaction at bottom of the storey
VEd is the total vertical load at bottom of the storey
H,Ed is the storey sway when frame loaded with
horizontal loads
h is the storey height
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Simple Modeling of Structures
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Simple Modeling of Structures
Limits on portal frames given in NOTE 1B & 2B of Clause5.2.1:
Note 1B: the portal rafter slope is not steeper than 1:2
(26) Note 2B: the axial load in the rafters or beams is not
significant. when
EdN. or rearrange o .cr
NEd
y
N3.0
, cr
2EI=
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Simple Modeling of Structures
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Simple Modeling of Structures
10cr
= FF
cr ifStrength design using 1st order elastic analysis
Axial loading is so low that no instability of membersor the frame would occur.
Neglect equivalent imperfections or fictitious forces.
From EC 3 cl. 6.3.1.2 simple compression (1) is
appropriate for a member with Ncr/NEd 25.
Need to check EC 3 equation (5.3) for in-plane beamAf
EdN,
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Simple Modeling of Structures
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p g
If 103
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p g
If 3
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p g
,
such as
Strength design using 1st order plastic collapse analysis.15
cr
be ignored in the analysis.
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nd Order Effects in Portal Frame
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Order Effects in Portal Frame
he framing spacing is 10m c/c, and 1/200 equivalent
horizontal load was applied.
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Method 1: Buckling Analysis
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g y
theoretical buckling strength of the portal frame.
an eigenvalue buckling analysis of a column will matchthe classical Euler solution.
The design load and constraints were used to calculate
the eigenvalue, because each load has an associatedbuckled mode.
he software ABAQUS was used to analysis the
buckling model
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Eigenvalue from buckling analysis
crFloadBuckling
Eigenvalue ===
Ed
oaes gn
he boundary conditions:
column base is pinned; All the beam-column joints are rigid;
The torsion & out-of-plan rotation of rafter is constrained;
the out-plan displacement of crane beam is limited.
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Buckling Modes
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3 first buckling modes are shown for demonstrationIncluding horizontal loads to simulate global imperfections
.
1,
=
cr
.
,2
=
cr
.,3=
cr
Beam, Column, Column,
in-plane buckling Out-plane buckling Out-plane buckling
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Method 2: Eq. 5.2 in EC3
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Limits on portal frames using formula 5.2
Slope of rafter: (15.12-13):21.5=1:10 (5.5) is less than
26, the formula is available.
The largest axial load of rafter is 50kN, and the elastic
critical load of thus rafter is 1843kN.
So,09.0027.0
1843
50
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Taking Equivalent Horizontal Loads into account to simulate
global imperfection:
kN3.11200
2256
200
loadverticalEHF ==
=
2.2kNF1detailedFor
==
.
F2
F1
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Method 2: Eq. 5.2 in EC3
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H,Ed is calculated by the software, and
mm49EdH, =
So,33.1
130001===
hHEd
cr
EdH,Ed
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Method 3: BS 5950-1
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This method is based on the plastic analysis, and wasused in BS 5950. (see reference)
For simplified, the axial load is calculated by software.
2 9
2342
37
492
316
D E
250
558B
Axial load (kN)A
F
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For the left hand bay (ABC):
Ic = 14300cm4 Pc =250kN
= 4 =r r
Lr= 16.078m
276.1422.8
078.16
21400
14300===
h
L
I
IR r
r
c
2.1
3
= r
cr
EI
0.2102142103
.
9
==
rrcr
R
16078200003.0842210250276.1
.116078 3
+
+
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For the right hand bay (DEF):
Ic = 126000cm4 Pc =505kN (conservatively)
= 4 =r r
Lr= 20.36m
8.413
36.20
41100
126000===
hIR r
r
c
3.02.1
1
3
+
+
=
rrcr
r
cr
LphpL
I
51.11041121039
==20360340003.01013505
8.4
.120360 6
+
+
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Three method were used to calculate the factor cr
Method 1:29.1=
cr
Method 2:
Method 3:33.1=
cr51.1==
crcr
e ac or cr s ess an , an e secon or er e ec smust be considered in design.
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Shear resistance
Ben ng moment res stance
Compression resistance.
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The design shear force is denoted by VEd (shear force design
effect).
The design shear resistance of a cross-section is denoted by
c, p ,
elastic distribution of shear stress.
The design shear force, VEd, should satisfy:
1.0V
Ed
,
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p ,
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p ,
e usua approac s o use e p as c s ear res s ance
Vpl,Rd in practice
The plastic shear resistance is essentially defined as theyield strength in shear multiplied by a shear area A
The yield strength in shear is related the yield strength in
yf
A
M0
V
Rdpl,
3V
=
.0=M
For BS 5950, Pv = 0.6pyAv
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The shear area Av is in effect the area of the cross-
section that can be mobilized to resist the design
redistribution.
For sections where the action is applied parallel tothe web, this is essentially the area of the web (with
some allowance for the root radii in rolled sections).
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EC 3 BS 5950Rolled I and H sections,load parallel to web
Rolled I, H and Channelsections, load parallel to web
wwfwfv r ++=
SS)toNto(refer1.0= Av = tD
Rolled channel sections,
trtbtAA 2 ++=
oa para e o we
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EC 3 BS 5950
e e , ox sect ons,load parallel to web
= th SStoNtorefer1.0=
Welded I, & box sections,load parallel to web
Av = td
Welded I H & box sections
=
wwv
thAA load parallel to flange
Av =2 td
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EC 3 BS 5950
Rectangular hollow sections,load parallel to depth
Rectangular hollow sections,load parallel to depth
)( hbAhAv += / Av =AD(D+B)
Rectangular hollow sections,
)( hbAbAv += /
oa para e to w t
Circular hollow sections
/2=
=
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- -bending) and member buckling resistance must bechecked, i.e.
Cross-section check (In-plane bending)Rdc,Ed MM
Member-buckling checkb,RdEd MM
MEd = design bending moment
Mc,Rd = design bending resistance about one principal axis
of a cross-sectionM = desi n bucklin resistance moment,
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EC 3 BS 5950
Class 1 & 2 cross-sections: Class 1 & 2 cross-sections:
=fW
c y . y
0M
Rd,plRd,c MM
==
C ass 3 cross-sect ons: C ass 3 cross-sect ons:
Mc = pyZ
ymin,le
Rd,ElRd,c
fWMM ==
Class 4 cross-sections:
or
Mc =pySeff1.2pyZ
0M
Class 4 cross-sections:
M = Zymin,eff
Rd,cfWM =
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Subscripts are used to differentiate between the plastic,
elastic or effective section modulus.
Plastic modulus Wpl (S in BS 5950)
Elastic modulus Wel (Z in BS 5950)
Effective modulus Weff (Zeff in BS 5950)
The partial factor M0 is applied to all cross-section bending
resistances , and equal 1.0.
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When the design value of the shear force is less than 50% of
the design plastic shear resistance, i.e. VEd0.5 Vpl,Rd, its
.
When the design value of the shear force exceeds 50% of the
design plastic shear resistance i.e. VEd> 0.5 Vpl,Rd, the yield
strengthfyshould be reduced by (1 r) in the determination
, c,Rd.
yyr ff )1( =
2
12 = EdVwhereRdpl,
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EC 3 BS 5950When, VEd > 0,5Vpl,Rd
When, Fv > 0.6 Pv
available to determine thereduced design plastic
or ass or cross sect ons
Mc =py (S Sv)
res stance moment or c ass 1
and 2 I-sections. For Class 3 semi-comp
sections
Mc =py (S Sv/1.5)
0
)0.25(
M
ywwRdypl
RdyV
ftAWM
/,,,,
=
or ass s en er sec ons
Mc =py (Zeff Sv/1.5)RdycRdyV MM ,,,, But
Where, = [2Fv/Pv 1.0]2
, www2
12
= EdV
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Rdpl,
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follows:
RdtEdt NN ,, (Tension check)
Nt,Ed is the tension design effect
N is the design tension resistance,
Design tension resistance Nt Rd is limited either by:
Yielding of the gross cross-section Npl,Rd
- u,R
Whichever is the lesser.
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or mem ers connec e y we ng
Desi n tension resistance N is e ual to the ield,
strength of the cross-section, Npl,Rd
,
y
Rdpl
AfN =
A is the gross area of the cross-section
M0 = 1.0 from Singapore NA
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For members connected b boltin , N is reduced due to,holes and is the lesser of:
1. Yield resistance of gross section
0
Rdpl,y
AfN
=
2. Ultimate strength of net section
M2
unet
Rdu, 9.0
fAN =0.9 is a reduction
factor for
ne the cross-section
eccentricity, stress
concentration etc
u
tension strength
M2 is the partial factor for fracture, and
M2 = 1.10 in Singapore NA
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The Net Area of the cross-section is the
gross areadeduction for bolt holes
For each fastener hole, deduction is the
ross cross sectional area of the hole
Angles connected through one leg;
T sections and channels connected through outstands
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When the fastener holes are not sta ered, the total area tobe deducted for fastener holes should be the maximum sum
of the sectional areas of the holes in any cross-section
.p1
e2=p2
net 0B
n = number of holes0 ae c ness t
t
net
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Wh f t h l t d th t t l t b d d t d i th
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When fastener holes are staggered, the total area to be deducted is the
1. The area for holes crossing a perpendicular cross section
2. the sum of the areas of all holes in an dia onal or zi -za line acrossthe member less s2t/4p for each gauge space in the chain of holes
s
s
d0 b a
- , 0
On section a-b, Net Area = A 2d0t s2
t/4p
Net cross-sectional area is the lesser of:tnnet 0=
=
s2
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ne
4
BS 5950 EC 3
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BS 5950 EC 3
Tension resistance
RduRdplRdt NNN ,,, ;min=
Tension capacity
AP =
0
Rdpl,
M
y
AfN
= Ae is the sum of the effective net area ae
M2
unet
Rdu, 9.0
fAN =
e n g
For grade S275: Ke = 1.2
tndAAnet 0=For grade S355: Ke = 1.1
For grade S460: Ke = 1.0
tndAAnet 0=
2
Staggered
fastenersMIN
e s . y
a is the ross area of the element
= p
ndtnet4
0an is the net area of the element
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The desi n value of the com ression force N ateach cross-section shall satisfy:
RdcEd ,
For Class 1, 2 & 3 cross-sections
Unaffected by local buckling
Design compression resistance Nc,Rd equals theplastic resistance Npl,Rd:
0M
y
Rdc
N
=,
M1 = 1.00, in NA to SS EN 1993-1
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For Class 4 sections: Local buckling of Class 4 prevents the attainment of
the squash load
es gn compress on res s ance m e o oca
buckling resistance,
0M
yeff
RdcN
=,
Aeffis the area of the effective cross-section
If Class 4 section is unsymmetrical, it has to be designed
as beam-column due to the additional moment arising.
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76 CSP 08 - 2012
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Web bearing and buckling
Resistance to transverse forces
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Web Bearing and Web Buckling are modes of failure that
arise from concentrated forces being transversely applied
.
Web bearing (a) and buckling (b) failure modes
a b
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Plate Stiffener
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79CV3202 CSP 08 - 2012 79DOUBLE STRUT WITH SPLAY
Strut-Waler Connection with Plate Stiffener
Plate Stiffener
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Waler Flange
StrutWaler
80CV3202 CSP 08 - 2012Waler Web
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most vulnerable location, close to the root radius at the
junction of the web and flange where the force is
concentrated.
Buckling happens when the web behaves like a slender
. ,is assumed that the web is adequately restrained by the
flange to which it is connected in the lateral direction, and
therefore, the web can neither rotate nor move laterally.
81 CSP 08 - 2012
Design Treatment is very different from
current Approach
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- requ res a wo n epen en c ec s are carr e
for web bearing and buckling.
EC3 resents a sin le check to deal with these two failure
modes. This single check accounts for the bearing and
uc ng o t e we w en t e mem er s su ecte to a
transverse force.
82 CSP 08 - 2012
Resistance to Transverse Force
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EC1993-1-5 distinguishes between two types of forces applied
through a flange on to the web:
i) forces resisted by shear in the web [load types (a) and (c)]
flange [load type (b)].
83 CSP 08 - 2012
Load T es & k
Buckling coefficients for different types of load application
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If there are no web stiffeners, a=, hw/a=0
84 CSP 08 - 2012
Web Failure
For load type (a) and (c) the web is likely to fail as a result of:
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i. Crushing of the web close to the flange accompanied by
yielding of the flange.
ii. Localised buckling and crushing of the web beneath the
flange, the combined effect sometimes referred to as web.
85 CSP 08 - 2012
Web Failure For loading type (b) the web is likely to fail as a result of:
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. e rus ng;
ii. Buckling of the web over most of the depth of the member.
86 CSP 08 - 2012
Web Bucklin Failure
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87 CSP 08 - 2012
Resistance to Transverse Force
For unstiffened or stiffened webs the design resistance to
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tf
1
RdF
=
Where, tw is the thickness of the web;
yw
M1 is the partial factor for resistance of members
(M1 = 1.0 in SG National Annex)
Leff is the effective length of web.
88 CSP 08 - 2012
Effective Len th for Resistance
h ff ti l th f b h ld b d t i d f
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he effective len th of web should be determined from:
eff= f y
where, f is the reduction factor due to local buckling
y s t e e ect ve oa e engt , appropr ate to t elength of the stiff bearing ss.
89 CSP 08 - 2012
Stiff Bearin Len th
The stiff bearing length ss
on the flange should be taken as the
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sdistance over which the applied load is effectively distributed
at a slope of 1:1
ss is less than hw
90 CSP 08 - 2012
Stiff Bearin Len th
The stiff bearing length is not given in EC3; it can be calculated
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r s
Ss Ss
ss=t+1.6r+2T ss=t+1.6s+2T
91 CSP 08 - 2012
Stiff Bearin Len th
If the bearin surface of the a lied load rests at an an le on
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If the bearin surface of the a lied load rests at an an le onthe flange surface, as shown below, ss should be taken as
zero.
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Effective Loaded Len th
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y
calculated as follow:
For type (a) and (b)
but l distance between adjacent transverse
21 mms fsy =
stiffeners.
93 CSP 08 - 2012
Effective Loaded Len th
y
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y
value of the following equations.
2
2
1 mlmtll efey +++=
mmtll ++=
2
Where, cshf
l s
wyw
wFe +=
2
94 CSP 08 - 2012
Non-Dimensional Factors m & m
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wyw
fyf
tfm =1
where,fyf is the yield strength of the flange
fyw is the yield strength of the web
2
5.0if02.02 >
= Ff
w
tm
5.0if02
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F
w bh 2
sFaa
= .-.
, 1
distance between the loaded flange and the stiffener
This equation is valid for 3.0and,3.005.0 11 bb
And loading according to Type (a)w
96 CSP 08 - 2012
Lon itudinal Stiffener k
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+
= baIsl
s1
3
3
1,-3.0210139.10
awww
Where, Isl,1 is the second moment of area of the
stiffener closet to the loaded flan e includin
contributing parts of the web according.
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Reduction Factor
The reduction factor should be obtained from:
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The reduction factorF should be obtained from:
0.15.0
=F
F
ywwy ftl
crF F=,
w
w
Fcr
h
tEkF 9.0=
98 CSP 08 - 2012
Verification under Transverse Force
The verification should be performed as follow:
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The verification should be performed as follow:
0.12 =weffyw
d
tLf
1M
, e Leff is the effective length for resistance to transverse
forces;
tw is the thickness of the plate.
99 CSP 08 - 2012
Verification under Interaction
If the girder is subjected to a concentrated transverse
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If the girder is subjected to a concentrated transverse
force and bending , the combined effect should satisfy
the following:
4.18.0 12 +
Where, 0.11 =ply
Ed
Wf
M
0M
100 CSP 08 - 2012
Example - Resistance to Transverse
Force
Determine the resistance to transverse force of a 406 140 UB39
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Determine the resistance to transverse force of a 406 140 UB39
Grade S355 steel section under the type of load application shown
below:
ss = 50 mm
c = 2725 mm
5500 mm
101 CSP 08 - 2012
b
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b
z h = 398.0mm
r
f
b = 141.8mm
=
h dhw
w .
tf= 8.6mm
tw
s
r = 10.2mm
z
tf= 8.6mm
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The load application is type (a)
,
a=, hw/a=0
2
=
= hw
aF
103 CSP 08 - 2012
-
tw3
=
hwFcr .
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hw
4.6 3
780649
8.380.
=
2.228.141355
1 =
== fyfbf
m
.wyw
5.0Assuming >F
39.2
8.380
02.002.0
22
2 =
=
= wh
m .
104 CSP 08 - 2012
y
( )
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( )mmtsl fsy 12 21+++=mm2022.392.2216.8250 =+++=
ywwy ftl
3554.6202
crFok
..780649
==
105 CSP 08 - 2012
5.0
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5.0=
F
F
0.165.077.0
5.0
== ok
mmlL yFeff 13120265.0 ===
tLfF
weffyw=
kN
M
298104.6131355 3-
1
==
.
106 CSP 08 - 2012