Managing distortion in welded structures using FEM
Transcript of Managing distortion in welded structures using FEM
Managing distortion in welded
structures using FEM
MEHDI GHANADI
Master of Science Thesis in Lightweight Structures Dept of Aeronautical and Vehicle Engineering
Stockholm, Sweden 2013
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MASTER THESIS PROJECT
Managing distortion in welded structures using FEM
Student:
Mehdi Ghanadi
Supervisor:
Dr. Zuheir Barsoum
A master thesis report written in collaboration with
Department of Aeronautical and Vehicle Engineering
Division of Light Weight Structures
Royal Institute of Technology
And
Volvo Construction Equipment Company
August 2013
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Table of Contents
1 Introduction ……………………………………………………………………. 5
2 Literature review………………………………………………………………… 5
3 Inherent strain …………………………………………………………………... 7
3.1 Inherent strain definition …………………………………………………… 7
3.2 Thermal history of inherent strain ………………………………………….. 8
3.3 Inherent strain distribution ………………………………………………… 10
3.3.1 Estimating formula for inherent strain distribution ……………........ 10
3.3.2 Determination of inherent strain zone from stress distribution ……. 11
4 Inherent Deformation …………………………………………………………. 12
5 Geometry and welding parameters …………………………………………….. 17
6 FEM Analysis ………………………………………………………………….. 18
6.1 Material properties …………………………………………………………. 19
6.2 Thermal analysis …………………………………………………………… 19
6.3 Mechanical analysis ………………………………………………………… 20
6.4 Large and small deformation theory ……………………………………….. 21
6.5 Elastic FEM analysis ………………………………………………………. 22
6.5.1 Inherent strain approach …………………………………………… 22
6.5.2 Inherent deformation approach ……………………………………. 23
6.5.3 Shrinkage force approach ………………………………………….. 24
7 Discussion ……………………………………………………………………… 26
8 Conclusion ……………………………………………………………………… 27
9 Recommendation for future work ……………………………………………… 28
10 References …………………………………………………………………….. 29
Appendix A: Experimental formula for inherent strain distribution …………………... 35
Appendix B: Material Properties of S355 …………………………………………….. 36
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List of Figures
Figure 1: Displacement State under (a) Standard state (b) Stress State(c) Stress Released
State………………………………………………………………………….……… 7
Figure 2: Restrained condition in general case …………………………………….. 9
Figure 3: Temperature history, stress and strain of bar C under different thermal
condition……………………………………………………………………………. 9
Figure 4: Inherent strain distribution by FEM…………………………….……….. 11
Figure 5: Inherent strain zone estimation by residual stress distribution…………… 12
Figure 6: Classification of welding distortion …………………………………….. 12
Figure 7: Inherent deformation components ………………………………………. 13
Figure 8: Inherent deformation components ………………………………………. 13
Figure 9: Inherent Strain Zone …………………………………………………….. 15
Figure 10: Longitudinal and Transverse deformation …………………………….. 15
Figure 11: Tendon(shrinkage) Force ………………………………………………. 17
Figure 12: T-joint: geometry and boundary condition …………………………….. 18
Figure 13: Temperature profile at weld toe ……………………………………….. 20
Figure 14: Thin plate ……………………………………………………………… 21
Figure 15: Inherent deformation and inherent bending distribution in T-joint …… 23
Figure 16: Inherent force distribution along inherent strain zone ………………… 24
Figure 17: Transverse shrinkage force ……………………………………………. 25
Figure 18: Longitudinal and transverse deflection by elastic and elastic plastic FEM … 25
Figure 19: Isometric and top view of a T-Joint ……………………….…………… 35
Figure 20: Material Thermal and Mechanical Properties…………………………… 36
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List of Tables
Tabel 1 : Process of production of inherent strain ………..…………………………….. 10
Tabel 2 : Inherent strain distribution by FEM and experimental formula ……………… 10
Tabel 3 : Welding parameters …………………………….…….…..………………….. 18
Tabel 4 : Inherent deformation components by three inherent based methods ………... 26
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1-Introduction
Welding as high productive joining method is widely employed in automotive, aerospace and
shipbuilding industries. In practice, welding distortion brings about undesirable effects on
production accuracy, appearance and strength of welded components. Thus, in order to
increase the productivity and decrease the cost of the product, prediction and analysis of
welding deformation are key factors in industrial context.
Distortion of a structure can be measured experimentally; whilst in case of large or complex
structures it is expensive and also time consuming. Numerical analysis is then performed
using finite element method (FEM) that reduces the cost; however, in case of large welded
structure and considering extremely nonlinear mechanical behavior of welding the
computational expense incurred which must be cut through elastic analysis. In this sense, the
residual plastic strain, namely inherent strain as a source of residual stress and welding
distortion should be analyzed.
The purpose of this study is to detail the prediction procedure of deformation in welded
structure by elastic finite element modeling using inherent strain method. As a matter of fact
inherent strain as an inelastic permanent strain or residual plastic strain, which exists in
vicinity of fusion zone, is responsible for welding deformation and residual stresses.
Comparing with elastic plastic analysis, inherent strain method has less computing time
however the state of welding may be not investigated in detail; Furthermore, appropriate
assumption of inherent strain region and determining the accurate values of inherent
deformations in each typical joint bring about some limitations. On the other hand, just the
elastic modulus and Poisson’s ratio at room temperature is used in elastic FEM, and there is
no need for temperature material properties. So, at the present time, thermal elastic plastic
finite element method can be used to predict residual stresses and welding deformations in
small or medium structures but for large components elastic FEM is promising method.
2-Literature review
In search of welding distortion many studies were carried out in past decades [1-7]. For small
and medium welded structures some investigations have been developed, using elastic plastic
FEM [8]. However, for large components this method is computationally burdensome that
leads to the purpose for elastic FEM, for which the inherent strain method is used. For seeking
inherent strain properties, Ueda et al. [9] developed an estimating formula and also introduced
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some series functions to predict inherent strain zone. By using the inherent strain theory,
Murakawa et al. [10] introduced the elastic finite element method. In this sense, Murakawa
also developed the in-house code JWRIAN to simulate the welding deformation during all
process of welding assembly of a welded structure. Thereafter the elastic method has become
of great interest especially in shipbuilding industries where computational time is a key factor
in analyzing of large welded structures. Furthermore, thin plate welded structures with low
stiffness property bring about more severe problems in welding distortion. In this sense, by
using elastic FEM and applying inherent strain as initial strain, the welding distortion of
asymmetric curved block [11] and also plate bending in ship hull curved plate [12] were
analyzed. Meanwhile, Nair [13] also studied about principal bending and twisting deformation
in ship structures. Considering parametric studies, Murakwa[14,15] also investigated the
influence of welding sequence and restrained condition. In their research work contact
condition is also analyzed by introducing interface element in fusion zone. LUO and his co-
workers [16] proposed a theoretical formula to calculate inherent strain distribution and
thereby deformation, considering the effects of high temperature and restrained condition.
Significant reduction in computational time is also of great interest. In this sense, Murakawa
[17, 18] performed iterative substructure method(ISM) on a bogie beam and also developed
an efficient three dimensional approach for residual stress estimation, using block dumping
method. In line with time simplification, Bachorski [19] and Deng [20] also introduced
shrinkage volume method, as contraction force, but limited to special materials. Saenz and his
co-workers [21-31] did a lot of effort in field of inherent deformation. In their research works,
inherent deformations and influential parameters, like plate dimension, side and edge effects
were completely studied. Wang [32] also analyzed buckling mode, as most critical welding
deformation for thin plate structures using inherent deformation. In order for inherent
deformation to be determined, an experimental approach namely inverse analysis was also
undertaken [33-36]. This method is reliable as it allows for measurement on some small
selected points to be directed on a path to a more accurate result. Shrinkage force method is
also another applicable approach in welding deformation analysis. Many efforts have been
done in different working areas like shipbuilding industries [37] and also in railway vehicles,
applied on bogie frame [38]. Recently, Asifa khuram et al [39] applied equivalent load to
calculate welding deformation of a butt welded joint, using integration of inherent strain
component along welding line. Good agreement with the experimental results was achieved in
their results.
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In general each of the previous works has been focused on one of the inherent strain based
approaches. However, deciding on choosing the proper methods leads to compare them that
are the main focus in this study. So in this sense, elastic FEM based on three inherent strain
based methods found in the literature, is analyzed and the resulted welding distortions are
compared. This is based on thermo elastic plastic modeling, which makes use of block
dumping approach in mechanical analysis to predict inherent strain in longitudinal and
transverse directions.
3-Inherent strain
3-1- Inherent strain definition
In order to describe the inherent strain we can consider a body under three different states. In
first case, name as standard state, there are neither external forces nor internal stresses. In the
second case, the body is under residual stress state and in the last one there is stress released
condition in which the elements are separated.
As stated by small deformation theory and considering , and ∗ as distance between two
nodes in standard state, stress state and stress release state respectively. The strain among
these states can be defined as follow [40]:
1
∗∗
2
(a) (b (c)
Figure 1.Displacement State under (a) Standard state (b) Stress State (c) Stress Released State
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∗
3
In above formulas, , ∗ and are total strain, inherent strain and elastic strain respectively.
So we can say:
∗ 4
Thus the inherent strain is responsible for deformation (inherent deformation) and residual
stresses in the body. Besides, total strain consists of some strain components which produce
with different process. These strains can be explained by:
5
Where , , and represent plastic strain, thermal strain, creep strain and phase
transformation strain correspondingly. So, from the expression of inherent strain the above
equation is written as below:
∗ 6
It should be noted that the thermal strain disappear when temperature comes back to room
temperature. Besides, the solid-state phase transformation strain itself causes two other kind
of strains name as transformation strain resulted by volumetric strain and transformation
plasticity strain. For low carbon steel, because of small dilation resulted by martensitic
transformation and high transformation temperature, the phase transformation has less effect
on residual stresses and deformation so in this case the phase transformation strain can be
neglected. But, for medium carbon steel because of large dilation and low transformation
temperature range, phase transformation strain should be taken into account [20, 41].
3-2- Thermal history of inherent strain
Temperature distribution is classified into high temperature zone near the heat source and low
temperature field in the vicinity area. Assuming Young’s modulus E and yield stress ,
mechanical behavior of welded structure can be simulated by three different bars named as
central bar C and two side bars S representing the high temperature region and adjacent area
respectively [33,10].
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Figure 2. Restrained condition in general case
Noting that the surrounding zone (bar S) plays as a constrained role, like elastic spring, for the
high temperature area (bar C). As a general case that is shown in above figure, bar C is
restricted by bar S via movable rigid body condition.
Fig.3 is used to draw conclusions about when inherent strain is produced. The diagram plots
stress and strain versus temperature. Magnitude of maximum temperature and also yield
temperatures, and , are influential, and their importance is seen in the diagram.
Further to above graph, in process one 0 → → 0 , which represents low
temperature heating, plastic strain and residual stress are not created. However, during second
process (0 → 2 → 0 , residual stress which produced in cooling step is
resulted by residual plastic strain ∆ , or inherent strain, induced in heating stage. As
indicates in process three 0 → 2 → 0 residual plastic strains are induced
both in heating and cooling steps ∆ , ∆ , thus then inherent strain is summation of these
two residual plastic strains ∗ ∆ ∆ . To sum up, correlation among plastic strain,
Figure 3.Temperature history, stress and strain of bar C under different thermal condition
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inherent strain, inherent deformation ∆ ∗ ∗ and residual stress is described in below
table:
Table 1.Process of production of inherent strain
Heating Process Low Temp. Medium Temp. High Temp.
2 2
∆ 0
∆ 0 0 2
∗ 0
∆ ∗ 0
0
3-3- Inherent strain distribution
In principle the distribution zone and magnitude of the inherent strain component are
governed by the highest heating temperature and the constraint conditions [14]. Two methods
are studied in this section, one based on experimental formula and the other is corresponding
to residual stress distribution.
3-3-1-Estimating formula for inherent strain distribution
Based on average temperature rise,T with respect to heat input, and specific heat, , Yukio
Ueda et al.[42] developed an experimental formula to determine the magnitude and
distribution of inherent strain zone. In their study, the effect of structural geometry and its
material property is also taken into account. As may be seen in below table, for a T-fillet joint,
the width of inherent strain distribution, and magnitude of inherent strain, ∗ , are
calculated by proposed formula (Appendix A). As it is seen, experimental formula and results
by FEM are in good agreement.
Table 2.Inherent strain distribution by FEM and experimental formula
Weld
type
By F.E.M By Formula
∗ ∗
T‐Joint 108.6 44 2.06 10 42 2.8 10
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Fig.4 shows the inherent strain distribution in middle cross section of a T-joint. As can be
seen for T-joint from almost 44 mm away from center line, the inherent strain is almost zero.
Noting that, inherent strain region is varied along welding line. So as a good estimation the
average value of inherent strain zone should be calculated.
3-3-2-Determinationofinherentstrainzonefromstressdistribution
Inherent strain zone may also be determined by residual stress distribution. As illustrated in
Fig.5, in case of thin plate welded structures, inherent strain is dispersed through the whole
thickness so it thus becomes evident that just the width of inherent strain zone is important,
however for thick plates, strain distribution inside the thickness should also be taken into
account [9]. As shown in Fig.5, by comparing the residual stress distribution with inherent
strain distribution, Fig.4, the inherent strain zone can also be determined.
Figure 4.Inherent strain distribution by FEM
10
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3-Welding deformations
4-Inherent Deformation
Basically there are six types of welding deformation namely as: longitudinal shrinkage,
transverse shrinkage, longitudinal bending, transverse bending (angular distortion), rotational
distortion and buckling distortion [43].
Figure 6.Classification of welding distortion
Figure 5.Inherent strain zone estimation by residual stress distribution
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The first four deformations also called inherent deformations and the last two are resulted
from these inherent deformations.
In order to analyze the inherent deformation, first by using a simple method the transverse
shrinkage, longitudinal shrinkage and angular distortion are described. In an attempt to do
that, as shown in Fig.8 a simple T-joint welded structure is considered. So the transverse
shrinkage can be calculated by making the difference between displacements of lines A and B
in transverse direction [44].
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Where:S: Transverse shrinkage; , : Displacement of line A and B in transverse
direction.
Figure 8.Inherent deformation components
Figure 7.Inherent deformation components
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Similarly by following equation the angular distortion can be calculated through deflection
distribution.
arcsin 8
arcsin 9
Where is angular deflection and , and are displacement of line C, D and E
respectively. is also displacement of line B in transverse direction.
Longitudinal shrinkage is also expressed by shrinkage force in longitudinal direction name as
tendon force. Tendon force is defined with respect to the inherent deformation by below
formula:
∗ 10
Where ∗ represents the inherent strain in longitudinal (welding) direction. So in order to
transform inherent deformation into inherent strain the equations are analyzed on a fillet
welding joint. In this sense the relation between heat input and longitudinal inherent strain is
calculated by following formula [45,46]:
22
22
11
2 2 12
∗ .. . .
13
∗ .. . .
14
WhereQ , ε∗ and h are heat input, longitudinal inherent strain and thickness respectively.
Indexes ‘bs’ corresponds to base plate and ‘st’ is related to stiffener. Q and Q are heat input
for left side and right side of the baseplate. Accordingly the transverse inherent strain is
calculated by following equation:
15
∗2
∗ 15
The amount of curvature is also calculated based on angular distortion. So there is:
∗
2
16
For elements in inherent strain zone, one can explain the distribution of longitudinal and
transverse shrinkages by their corresponding inherent deformations. Following figure shows
this relation on deformed rectangular element.
∗ ∗
∗ ∗
x
z z(welding direction)
x
∗ ∗
a
b
Figure 9.Inherent Strain Zone
Figure 10.Longitudinal and Transverse deformation
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For thin plate structures longitudinal shrinkage, transverse shrinkage and angular distortion
are mainly produced by longitudinal and transverse inherent strains ∗ and ∗. By constitutive
equation longitudinal and transverse inherent stresses can also be calculated as follow:
∗1
∗ ∗ 17
∗1
∗ ∗ 18
The deformation of the plate is expressed using the inherent deformation method which
consists of integration of inherent strain over the cross section of the plate and perpendicular
to welding line. The inherent deformation can be divided into four components; Longitudinal
shrinkage ( ∗), transverse shrinkage ( ∗), longitudinal bending ( ∗), and transverse bending
( ∗), that are defined by the following equations [47, 48]:
∗ 1 ∗ 19
∗ 1 ∗ 20
∗ 1 ∗ 21
∗ 1 ∗ 22
In which means plate thickness and moment inertia (I) defines as bellow:
112
23
It is supposed that inherent strain components are uniformly distributed along welding line so
one can use the average values of inherent deformations which are calculated as follow:
∗ 1 ∗ 24
∗ 1 ∗ 25
17
∗ 1 ∗ 26
∗ 1 ∗ 27
In above formulas and are specimen length and weld length respectively; ∗, ∗ , ∗ and ∗ are also average values of corresponding inherent deformations. Longitudinal inherent
shrinkage can also be expressed by longitudinal shrinkage force ( ∗) named as tendon force.
∗ ∗ ∗ ∗ 28
Other components of Inherent force and moments in longitudinal and transverse directions
can also be defined as follow:
∗ ∗ ∗ ∗ 29
∗∗ 30
∗ ∗ 31
5-Geometry and welding parameters
The method of experiment is to conduct welding distortion, where T-fillet joint is used. The
specimen which made of S355 steel, both for base material and filler, represents a good
similarity with large structure. The temperature dependent thermo-mechanical properties of
S355 are found from Bhatti and Barsoum [49]. The dimensions and boundary condition are
shown in Fig.12. As can be seen, for both base plate and stiffener the thickness of 8mm is
chosen. Besides, during welding the baseplate has been clamped in one side and in 60 mm
from center of the baseplate. The welding parameters are detailed in table.3.Welding is
T
L
Figure 11.Tendon(shrinkage) Force
18
performed in such a way that firstly the stiffener is tack welded to baseplate. Then the
complete weld is performed by TA-1400 robot consists of LNM MoNiVa 1.2mm filler wire.
Welding order has been conducted according to direction shown in Fig.12. In so doing, the
opposite side of clamped area is welded and thereafter cooled to the ambient temperature. In
next step, by keeping the same welding direction and weld start/stop location the clamped side
is welded and then the whole structure is cooled to ambient temperature.
Table 3.Welding parameters
Throat
(mm)
Current
(I)
Voltage
(V)
Weld length
(mm)
Travel Speed
(mm/s)
Weld passes
T-Joint 4 390 30 300 13.3 1
6-FEM Analysis
In order to calculate the deformation in welded structure a three dimensional finite element
model has been employed by using ANSYS. Both models are meshed with 8-node solid 70
linear elements. The FE mesh was created in a way to give high accuracy, that it was finer as
it approached the heat affected zone (HAZ). A finer mesh increases accuracy, but the
computational expense increases must be cut through an educated estimation of the HAZ
Figure 12.T‐joint: geometry and boundary condition
19
region. Thus a mesh density gradient can shorten the time while maintaining accuracy.
Thereafter by using thermal mechanical uncoupled formulation, thermal and mechanical
behavior of structure is analyzed. In fact, insignificant dimensional changes in welding
procedure and small mechanical work comparing with thermal energy resulted by weld are
the main reasons to use uncoupled formulation. Therefore thermal problem is analyzed
independently from mechanical part, however, using temperature dependent thermo physical
and mechanical properties make the formula as a combination of transient temperature field
and stress analysis.
6-1-Material Properties
The temperature dependent thermo physical and mechanical properties of S355 are obtained
from [13]. By using hook’s law and considering young modulus and poisons ratio that vary
with temperature the elastic strain is calculated. In order to calculate the plastic strain, the
material properties are modeled in such a way that bilinear hardening model is governed and
von misses stress as yielding criteria is also assumed.
6-2-Thermal Analysis
Deposition of filler material is investigated both in thermal and mechanical analysis to get
temperature and residual stress distribution respectively. In so doing, lumping method as a
highly time efficient heating technique is used [50]. Noting that, during welding just small
part of structure is molten and the rest are in solid condition. So in the heating region, thermal
process is analyzed and then the resulting temperature is dispersed over the rest of structure.
The rate of heat input is calculated based on arc current (I), arc voltage (U), welding speed
( ) and number of weld passes (n) by following formula [37]:
q 32
In above formula q is heat input per unit length j mm and η is the welding efficiency.
Correspondingly the total heat input is explained as follow [51]:
Q Q ηUI 33
20
Where Q is volumetric heat flux which is defined as bellow:
VηUI 34
In above formula V is the volume of block.
According to Newton’s law the heat loss resulted by convection is calculated as below [52]:
q h T T 35
In above equation h , T , T represent temperature dependent film coefficient, surface
temperature of weld joint and ambient temperature. It should be noted that in current study the
heat loss due to radiation is ignored. Generally there are three approaches to analyze the
deposition of filler material name as gradual weld bead deposition, rapid dumping and
lumping or block dumping [49]. In the current study lumping method as a highly time
efficient heating method is used. According to the welding sequence that is described in
section 5, the temperature profile at weld toe has been shown in Fig.13. As it can be seen the
maximum temperature of 1420 causes inherent strain distribution at vicinity of welding
area.
6-3-Mechanical Analysis
By thermal analysis the temperature distribution and its history is calculated. Thereafter the
temperature history is applied as a thermal load in mechanical elastic plastic analysis. In the
mechanical part, by keeping the same mesh as thermal analysis just element type is changed
to solid 185, which allow for three degree of freedom on each of its 8 nodes. As a matter of
fact when the deflection of plates becomes more than certain amount then the linear theory is
Figure 13. Temperature profile at weld toe
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not validated. Thus then with consideration of the large deformation theory, that causes
accurate results [44], the mechanical simulation has been performed. In this sense, the total
strain is composed of elastic strain ( ), plastic strain ( ) and thermal strain ( ):
The thermal strain disappears when temperature comes back to room temperature.
6-4-Large and Small deformation Theory
When the deflection of plates becomes more than certain amount then the linear theory is not
validated. In this condition the results show that the deflection of member is more than its
length which is incorrect. So by using large deflection theory the differential equation with
non-linear term must be solved. In order to describe this non linearity the equation related to
strain and displacement is investigated. For thin plates it is supposed that, total deflection
, is equal to deflection of mid-plane, , .So according to Mindlin plate theory
following formula is written[53].As can be seen in the below equations the first part related to
elastic strain and the second part represents non-linear behavior.
12
37
12
38
2 39
In above formula index ‘0’,’i’ and ‘b’ represent mid-plane, in-plane and bending conditions
respectively , and are strain in x and y directions; represent shear strain on x-y
x
y z
Figure 14.Thin plate
22
planes and u, v and w are displacements in x, y and z respectively. The curvature of plate is
also defined by following formulas:
40
41
42
Where and are curvature in plane parallel to x-z plane and y-z plane correspondingly
and as twisting curvature which shows the warping of x-y plane.
6-5-Elastic FEM Analysis
Elastic FEM may also be analyzed to reproduce the welding distortion. In so doing, just the
elastic modulus and Poisson’s ratio at room temperature are used, and there is no need for
temperature material properties. Thus by removing the nonlinear items, the computational
time decreases significantly. T-joint is meshed with shell 281 element where is more refined
in inherent strain zone. In elastic FEM three different inherent strain based approaches can be
introduced, which initial load condition is the main difference amongst them. In first case, the
inherent strain components are directly applied on inherent strain zone and then the elastic
FEM is carried out. Whilst, in the other two methods, firstly the inherent strain is integrated
over welding line then the results in the form of displacement and force, namely inherent
deformation and shrinkage force respectively, applied on inherent strain zone.
6-5-1-Inherent strain approach
The longitudinal and transverse inherent strain is calculated by elastic plastic analysis. As a
good approximation, the average value of inherent strain distribution is calculated along the
welding line and then the result is considered as inherent strain zone. Thereafter by equation
(44) the strain components are integrated over thickness (t) and the results applies on each
element in inherent strain zone. Therefore, by considering large deformation theory the
welding deformation is calculated by elastic FEM [9]. Noting that according to equation (43)
the magnitude of total strain consists of bending ( ) and membrane ( ) components. In this
sense, the in-plane and bending items causes in plane strain and curvature respectively.
23
6-5-2-Inherent deformation approach
As illustrated in fig.15, in inherent deformation approach, the average value of inherent
deformation components along welding line is calculated by equation (24-27) and the results
in the form of initial displacements apply on inherent strain zone and thereafter elastic FEM
carried out [32].
Figure 15. Inherent deformation and inherent bending distribution in T‐joint
24
6-5-3-Shrinkage force approach
Welding distortion can also be calculated by applying equivalent force and moments. In this
method, namely shrinkage force approach, by using equations (28-31) the longitudinal and
transverse inherent strains are integrated over cross section of welding line. Thereafter
according to fig.16 the transverse shrinkage force ( and transverse moment ( ) are
applied on inherent strain zone. Since the analysis is performed on flat plates, then the
longitudinal shrinkage force ( ) and longitudinal moment ( ) should just applied on the
nodes located at both ends of the plate [37-39, 54-56]. Noting that in order to get the loading
per node, the force should be divided by the number of nodes that exists in inherent strain
zone. Thereafter the nodal load has to be applied on each node and then carry out the elastic
analysis.
In search of shrinkage force method some experimental formulas are also introduced. As a
case in point according to White’s parametric study the longitudinal shrinkage force may also
be calculated by welding properties as below:
Where w is welding speed and η represents as arc efficiency. According to welding
parameters and also equation (45) the longitudinal shrinkage force is calculated as 123 KN
[8]. As can be seen in fig.17 and by using equation (29), the transverse shrinkage force is
calculated along the welding line.
Figure 16.Inherent force distribution along inherent strain zone
25
Distortion components calculated by three inherent strain based methods are compared in
fig.18 and table.4. It is seen that, considering the constraint conditions, the maximum
transverse bending and longitudinal bending occurs in front edge and side edge of the model
respectively. Table.4 shows the other two deformation components, as longitudinal and
transverse shrinkages. The outcomes are also compared with elastic plastic results and
experimental data.
Table 4.Inherent deformation components by three inherent based methods
T‐Joint Elastic Plastic Elastic
Inherent Strain Inherent Deformation Shrinkage Force
Longitudinal Shrinkage (mm) 0.622 0.324 0.40 0.41
Transverse Shrinkage (mm) 0.412 0.247 0.422 0.724
Angular Distortion (rad) 0.0107 0.0126 0.0139 0.0139
Figure 18.Longitudinal and transverse deflection by elastic and elastic plastic FEM
Figure 17.Transverse shrinkage force
26
7- Discussion
Thermo elastic plastic FEM and elastic FEM based on inherent strain theory are analyzed on
T-fillet joint and the derived deformations studied amongst that. Comparing these two
methods, nonlinear material properties in elastic plastic FEM leads to increasing the
computational time which is approximately 5 hours that is much longer than elastic FEM
which is less than 1 minute.
The residual stress and inherent strain both are predicted by block dumping and gradual weld
bead deposition methods have the same trends. Similar results are obtained in [49].Since less
computational time is the main objectives of inherent strain approach, so in this study the
block dumping as an efficient heating method has been chosen.
The requirement to determine inherent strain distribution is essential to perform elastic FEM.
Existence of such leads to purpose of inherent strain diagram, from which we can identify the
average value of inherent strain zone along welding line. Unsymmetrical distribution of
inherent strain, fig.4, is mainly resulted by constrained condition. The longitudinal and
transverse inherent strains, having been plotted on diagram, shows the maximum inherent
strain zone in the middle cross section of plate where maximum thermal gradient occurred. In
T-fillet joint the magnitude of transverse inherent strain is less than longitudinal component,
which corresponds to different constrained conditions in both models. It is also found that the
inherent strain zone, having been calculated by FE, is in good agreement with experimental
formulas. To precisely predict the welding deformation, one should make the average of
inherent strain region along welding line.
Inferences particular to the welding deformation are drawn from the inherent deformation and
shrinkage force graphs, which include inherent displacements, bending moments and
shrinkage force distribution respectively. Same as previous works [43], [47] in this study also
the sharp variation of data at entrance and exit of plate length, fig.15 and fig.17, namely edge
effect, causes undesirable results. Thus then, the average value of inherent deformation and
shrinkage force is calculated by removing some data located near to the plate edges.
For elastic plastic method, contact element has been defined between baseplate and stiffener
and also baseplate and the ground. This condition leads to introducing another nonlinear item
which increases the computational time. But, the results show that contact elements defined
27
between baseplate and ground prevents deflection through the ground that causes the out of
plane distortion to be increased.
Considering the out of plane deformation, Fig.18 and table.4, it can be seen that compared to
inherent deformation and shrinkage force methods, the inherent strain approach causes more
accurate results. This is an expected consequence considering the integration step in the first
two methods that leads to not properly estimation of the inherent strain distribution.
Bending deformation caused by residual stress gradient across the plate thickness effects on
angular distortion. In T-joint the bending moment is a more influential factor in out of plane
deformation rather than two other inherent components, longitudinal and transverse
shrinkages.
As shown in table.4, the transverse shrinkage and longitudinal shrinkage calculated in elastic
plastic simulation are in good agreement with same items calculated by inherent deformation
and longitudinal force methods respectively. It is because of the initial load condition as initial
displacement and force that are directly applied on inherent strain zone. Besides, it should be
noted that the restrained condition is also an important item where different constrained
condition may causes different result.
8-Conclusion
In this study the thermo elastic plastic FEM is performed to simulate the inherent strain and
welding distortion in a T-fillet joint. Thereafter, the elastic FEM based on inherent strain
approach and with different loading conditions, as initial strain, inherent deformation and
shrinkage force is simulated. Further to FEM and experimental results the following
conclusions are outlined:
Elastic FEM presents a reliable method by which to predict deformation, as well as
whether an elastic plastic method has been attained. In this sense, predicted welding distortion
in elastic FEM is in quantitative and qualitative agreement with elastic plastic method , i.e.,
out of plane deflection and angular distortion in both models. Besides, in elastic FEM the
computational time decreases significantly, which is almost the same for all three approaches.
In case of elastic plastic analysis the contact condition, especially between baseplate and
ground has influential role in welding deformation.
28
Out of plane deflection is well predicted by applying strain as initial load.
For in-plane deformation, the inherent deformation is reliable method to detect transverse
shrinkage. Both inherent deformation and shrinkage force methods are suitable to predict
longitudinal shrinkage.
9-Recommendation for future work
For effective application of elastic FEM in prediction of welding distortion the additional
works are suggested as below:
1-The elastic FEM performed in this thesis needs to be improved by parametric study. In
order to do so, the restrained conditions should be analyzed in detail. Furthermore, the relation
between bending deformation, heating parameters and plate thickness should also be
developed in the analysis.
2-In order to decrease the computational time, the iterative substructure method (ISM) can
also be implemented in elastic plastic FEM.
3-Inverse analysis based on inherent strain theory is also suggested to be performed. In this
experimental procedure the magnitude and distribution of residual stress is estimated as a
function of inherent strain.
29
10-References
[1] Martin Birk Sorensen, 1999,‘Simulation of welding distortions in ship section’ , Industrial
PHD thesis,Odense Steel Shipyard LTd., ,department of naval architecture and offshore
engineering.
[2] Artem Pilipenko, 2011, ‘Computer simulation of residual stress and distortion of thick
plates in multi-electrode submerged arc welding. Their mitigation techniques’, PHD Thesis,
Department of Machine Design and Materials Technology Norwegian University of Science
and Technology, Norway.
[3]T.L.Teng, C.Fung, P.Chang, W.Yang , 2001, ‘Analysis of residual stresses and distortions
in T-joint fillet welds’, Pressure Vessels and Piping J., Vol.78, pp.523-538.
[4]M.Hidekazu, D.Dean, R.Sherif, 2009,’Prediction of distortion produced on welded
structures during assembly using inherent deformation and interface element’, Transactions of
JWRI (Welding Research Institute of Osaka University), Vol.38, No.2, pp.63-69.
[5]L.Gannon, Y.Liu, N.Pegg, M.Smith, 2010, ‘Effect of welding sequence on residual stress
and distortion in flat-bar stiffened plates’, Marine Structures J., Vol.23, pp.385-404.
[6]Carlos Fabián Ajila Camacho, degree thesis,2008, ‘Study and control of distortion in
welded structural steel ‘, Polytechnic collage of Del litoral, GUAYAQUIL – ECUADOR.
[7] P.Michaleris, A.debiccari, degree thesis, ‘Prediction of welding distortion’, 12 th
symposium on zirconium in the nuclear industry,1998,Toronto,Ontario,Canada.
[8]D.Deng, W.Liang, H.Murakawa, 2007, ‘Determination of welding deformation in fillet-
welded joint by means of numerical simulation and comparison with experimental
measurement’, Materials Processing Technology J., Vol.183, pp.219-225.
[9] Y.Ueda, Ning-Xu MA, 1995,’ Measuring Method of three dimensional Residual stresses
with Aid of distribution function of Inherent Strain’, Transactions of JWRI, Vol.24,no.2
,Osaka University, Ibaraki, Osaka,Japan.
[10]Yu LUO, Hidekazu Murakawa, Yukio Udea, 1997, ‘Prediction of Welding Deformation
and Residual Stress by Elastic FEM Based on Inherent Strain(Report I)-Mechanism of
Inherent Strain Production’, Transactions of JWRI, Osaka University, Ibaraki, Osaka, Japan.
30
[11]D.Deng, Hidekazu Murakawa, Masakazu Shibahara, 1989, ‘Investigations on welding
distortion in an asymmetrical curved block by means of numerical simulation technology and
experimental method ‘, Computational Materials Sience J., Vol.48 , pp.187-194.
[12]Yukio UEDA,You Chul Kim,Min Gang Yuan, ‘A prediction method of welding residual
stress using source of residual stress (Report 1)’, Transactions of JWRI, Osaka University,
Ibaraki, Osaka, Japan.
[13] Madhu S Nair,Hidekazu Murakawa , 2002, ‘Theoretical study of forming of twisted T-
section longitudinal investigation from aspect of inherent strain (1st report)’,J.Kansai SOC.
N.A, Japan No.237.
[14]D. Deng, H. Murakawa, 2002, ‘Theoretical prediction of welding distortion considering
positioning and the gap between the parts’, International Offshore and Polar Engineering
Conference, Kitakyushu, Japan.
[15]H. Murakawa, D.Deng, N.Mafb, J.Wang, 2011, ‘Application of inherent strain and
interface element to simulation of welding deformation in thin plate structures’,
Computational Materials Science J., Vol.51, pp.43-52.
[16]LUO Yu, Deng Dean, XIE lei,2004, ‘Prediction of deformation for large welded
structures based on inherent strain’, Transactions of JWRI, Osaka University, Ibaraki,
Osaka,Japan,vol.33 ,No.1.
[17]R.Wang, J.Zhang, H.Serizawa, H.Murakawa, 2009, ’Study of welding inherent
deformations in thin plates based on finite element analysis using interactive substructure
method’, Materials and Design J., Vol.30, pp.3474-3481.
[18] Liang Wei, Itoh Shinsuke, Vega Adan,Murakawa Hidekazu,2006, ‘Numerical study of
inherent deformation produced in thick plate through bending by line heating’, Transactions
of JWRI, Vol.35,2006, No.1, Osaka University, Ibaraki, Osaka, Japan.
[19]A.Bachorski, M.J.Painter, A.J.Smailes, M.A.Wahab, 1999,’ Finite-element prediction of
distortion during gas metal arc welding using the shrinkage volume approach’, Materials
Processing Technology J , Vol.92-93, pp.405-409.
[20]Deng Dean, Luo Yu, Serizawa Hisashi, Shibahara Masakazu, 2003,’Numerical simulation
of residual stress and deformation considering phase transformation effect’, Transactions of
JWRI, Vol.32, no.2, Osaka University, Ibaraki, Osaka, Japan.
31
[21]Adan Vega Saenz, ‘Development of inherent deformation database for automatic forming
of thick steel plates by line heating considering complex heating patterns’, Doctoral Thesis,
Osaka University, Japan.
[22] Adan Vega, Sherif Rashed, Hisashi Serizawa, Hidekazu Murakawa, 2007, ‘Influential
factors affecting inherent deformation during plate forming by line heating (report 1)’,
Transactions of JWRI, Vol.36, No.1, Osaka University, Ibaraki, Osaka, Japan.
[23] Adan Vega, Hisashi Serizawa, Sherif Rashed and Hidekazu Murakawa,2008, ‘A
numerical study of parameters governing an inherent deformation database of plates formed
by line heating’, Joining and Welding Research Institute, Osaka University, Ibaraki, Osaka,
Japan.
[24] Adan Vega, Naoki Osawa, Sherif Rashed and Hidekazu Murakawa, 2010,’Analysis and
Prediction of Edge Effect on Inherent deformation of thick plates formed by line heating‘,
CMES, Vol.1802, No.1, pp.1-19.
[25] Adan Vega, Sherif Rashed, Yoshihiko Tango, Morinobu Ishiyama, and Hidekazu
Murakawa, 2008,’ Analysis and Prediction of Overlapping Effect on Plate Forming by Line
Heating ‘, Transactions of Asian Technical Exchanges and Advisory Meeting on Marine
Structure (TEAM).
[26] Adan Vega, Naoki Osawa, Yoshihiko Tango, Morinobu Ishiyama, Hisashi Serizawa,
Sherif Rashed ,Hidekazu Murakawa, 2008,’Effect of the Heating Model on the Prediction of
Inherent Deformation of Plates Formed by Induction Heating’.
[27] Adan Vega, Yoshihiko Tango, Morinobu Ishiyama, Sherif Rashed, Hidekazu Murakawa
‘Influential Factors Affecting Inherent Deformation during Plate Forming by Line Heating
(Report 3) – The Effect of Crossed Heating Lines’, Joining and Welding Research Institute,
Osaka University, Ibaraki, Osaka, Japan.
[28] Adan Vega, Yoshihiko Tango, Morinobu Ishiyama, Sherif Rashed, Hidekazu
Murakawa,’Influential Factors Affecting Inherent Deformation during Plate Forming byLine
Heating (Report 4) – The Effect of Material Properties’, Joining and Welding Research
Institute, Osaka University, Ibaraki, Osaka, Japan.
[29] Adan Vega, Masashi Nawafune, Yoshihiko Tango, Morinobu Ishiyama, Sherif Rashed,
Hidekazu Murakawa, ‘Influential Factors Affecting Inherent Deformation during Plate
Forming by Line Heating (Report 5) – The Effect of Water Cooling’, Joining and Welding
Research Institute, Osaka University, Ibaraki, Osaka, Japan.
32
[30] Adan Vega Saenz, Alexandra Lisbeth Camaño, Naoki Osawa, Ninshu Ma, Sherif
Rashed, Hidekazu Murakawa, 2011, ’ Influential Factors Affecting Inherent Deformation
during Plate Forming by Line Heating (Report 6) – The Edge Effect ’,International Workshop
on Thermal Forming and Welding Distortion, Bremen, April 06-07.
[31] Adan Vega, Yusuke Tajima, Sherif Rashed and Hidekazu Murakawa, Numerical Study
on Inherent Deformation of Thick Plates Undergoing Line Heating, Joining and Welding
Research Institute, Osaka University, Ibaraki, Osaka, Japan.
[32]Jiangchao Wang, Sherif Rashed, Hidekazu Murakawa, Masakazu Shibahara, 1989,
‘Investigations on buckling deformation of thin plate welded structures ‘, Osaka,Japan.
[33]Yukio Ueda, Hidekazu Murakawa, Ninshu Ma, 2012,’ Welding deformation and residual
stress prevention’.
[34]Y.P.Cao, N.Hu, J.Lu, H.Fukunaga, Z.H.Yao, 2002, ‘An inverse approach for constructing
the residual stress field induced by welding’, Strain Analysis for Engineering Design J.,
Vol.37, pp.345-359.
[35]Y.Ueda, M.Yuan, 1993, ‘Prediction of residual stresses in butt welded plates using
inherent strains’, Engineering Materials and Technology J., Vol.115, pp.417-423.
[36]Yukio Ueda, Ning-Xu Ma, 1995, ‘Measuring method of three dimensional residual stress
with aid of distribution function of inherent strain’, (Report III), Transactions of JWRI, Osaka
University, Ibaraki, Osaka,Japan,vol.24, No.2.
[37]P.Biswas, N.R.Mandal, P.Vasu, S.B. Padasalag, 2010, ‘Analysis of welding distortion
due to narrow-gap welding of upper port plug’, Fusion Engineering and Design J., Vol.85,
pp.780-788.
[38]Lu Yao Hui, WU ping bo, Zeng Jing, Wu Xing Wen, 2010,’Numerical Simulation of
welding distortion using shrinkage force approach and application ‘, Advanced materials
research J., Vol.129-131, pp.867-871.
[39]Asifa Khurram, Khurram Shehzad,2012,’FE simulation of welding distortion and residual
stresses in butt joint using inherent strain’, International Journal of Applied physics and
Mathematics, Vol.2,No.6, pp.187-194.
[40]A.Saenz, ‘Analysis and prediction of welding distortion using elastic finite element’,
Technology University of Panama.
33
[41]C.D.Jang, Y.S.Ha, D.E.Ko,2003, ‘An improved inherent strain analysis for prediction of
plate deformations induced by line heating considering phase transformation of steel’,
Proceedings of the thirteenth International Offshore and Polar Engineering Conference,
Honolulu, Hawaii, USA.
[42]Yukio Ueda, Min Gang Yuan,’A prediction method of welding residual stress using
source of residual stress’, (Report III), Transactions of JWRI, Osaka University, Ibaraki,
Osaka,Japan.
[43]W. Jiang, H. Murakawa, 2012, ‘An inverse analysis method to estimate inherent
deformations in thin plate welded joints”, Materials and Design J., Vol.40, pp.190-198.
[44]D.Deng, H.Murakawa, W.Liang, 2007, ‘Numerical simulation of welding distortion in
large structures’, Computer Methods in Applied Mechanics and Engineering J.,Vol.196,
pp.4613-4627.
[45]D.Deng, H.Murakawa, W.Liang, 2008, ‘Prediction of welding distortion in a curved plate
structure by means of elastic finite element method’, Materials Processing Technology J.,
Vol.203, pp.252-266.
[46]Wang Rui, Rashed Sherif, Serizawa Hisashi,2008 ‘Study on welding inherent
deformations in welded structural materials’, Transactions of JWRI, Vol.37, No.1, Osaka
University, Ibaraki, Osaka, Japan.
[47] Jiangchao Wang, Masakazu Shibahara, Xudong Zhang, Hidekazu Murakawa,2012
‘Investigation on twisting distortion of thin plate stiffened structure under welding’, Materials
Processing Technology J, Vol.212, pp.1705-1715.
[48] J.Wang, M.Shibahara, X.Xhang, H.Murakawa, 2012,’ Investigation on twisting
distortion of thin plate stiffened structure under welding ‘, Materials Processing Engineering
J., Vol.212, pp.1705-1715.
[49]Ayjwat A Bhatti, Zuheir Barsoum,2012, ‘Development of efficient three dimensional
welding simulation approach for residual stress estimation in different welded joints’, Strain
Analysis Journal.
[50]Y.Ueda, K.Fukuda, K.Nakacho, S.Endo, 1975,’A new Measuring method of residual
stresses with the aid of finite element method and reliability of estimated values’,
34
Transactions of JWRI(Welding Research Institute of Osaka University)., Vol.4, No.2, pp.124-
131.
[51] Zuheir Barsoum, 2008,’Residual Stress Analysis and Fatigue Assessment of Welded
Steel structures’, Doctoral Thesis.
[52] P.Biswas, M.M.Mahapatra, N.R.Mandal, 2009,’ Numerical and Experimental study on
prediction on thermal history and residual deformation of double sided fillet welding’,
Engineering Manufacture J., Vol.224, pp.125-134.
[53]Deng D., Murakawa H., 2008, ‘Prediction of welding distortion and residual stress in a
thin plate butt-welded joint’, Computational Materials Science J.,Vol.43, pp.353-365.
[54] Ship Structure Committee, 2008,’Welding distortion analysis of hull blocks using
equivalent load method based on inherent strain ‘.
[55] Chang Doo Jang, Yong Tae Kim, Young Chun Jo, Hyun Su Ryu, 2007,’Welding
Distortion Analysis of Hull Blocks Using Equivalent Load Method Based on Inherent Strain’,
10th International Symposium on Practical Design of Ships and Other Floating Structures
Houston, Texas, United States of America.
[56] Chang Doo Jang, Hyun Su Ryu and Chang Hyun Lee, 2004 ,‘Prediction and Control of
Welding Deformations in Stiffened Hull Blocks using Inherent Strain Approach’, 14 th
international offshore and polar engineering conference, Toulon, France.
35
Appendix A :Experimental formula for inherent strain distribution
The T-joint studied in this section is shown in below figure:
Average temperature rise, T is expressed by following formula:
TQρcA
47
In which Q, ρ, c, A are heat input, density, specific heat and cross-sectional area respectively.
Welding eccentricity β , as a dimensionless parameter shows the flexibility against to
longitudinal bending deformation due to welding, is expressed with respect to I, y, A as inertia
moment of transverse cross section, distance between weld center to the neutral axis of cross
section and cross section respectively.
βy AI 48
The width ( W )of distribution zone of inherent strain is calculated as below:
W0.484αE
cρ 2h h σ 49
In above formula, α, h , h denoted as the coefficient of linear expansion, thickness of
stiffener and base plate and σ shows yield stress of base plate.
The magnitude of inherent strain at weld metal related to W can be calculated as:
ε∗σE 50
Figure 19.Isometric and top view of a T‐Joint
36
Therefore by defining normalized factors a and b, the width and magnitude of inherent strain
are expressed as follow:
W aW 51
ε∗ bε∗ 52
In above formula, aand b are calculated as below:
a 1 0.27αET 1 β
σ 53
b 1 0.27αETσ
54
Appendix B: Material Thermal and Mechanical Properties of S355
Material thermal and mechanical properties of S335 is described in following graphs:
Figure 20.Material Thermal and Mechanical Properties