# Thermal and Residual Stress Distributions in Inconel 625 Butt-Welded Plates: Simulation and Experimental Validation

Authors: Harinadh Vemanaboina; Edison Gundabattini; Kaushik Kumar; Paolo Ferro; B Sridhar Babu
Journal: Advances in Materials Science and Engineering
 (2021)

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## Abstract

Thermal and residual stress distributions induced by the gas tungsten arc welding (GTAW) process on Inconel 625 were studied using numerical simulation and experiments. A multi-pass welding model was developed that uses a volumetric heat source. Thermomechanical analysis is carried out to assess the Thermal and residual stress distributions. Experiments were carried out with 5 mm thick Inconel 625 plates. X-ray diffraction techniques were used to measure residual stresses, and IR thermometry was employed to capture the temperature values on the welded joints. Simulations were performed with ANSYS numerical code, and a close agreement was found between the predicted and experimentally measured residual stress. Thermal measurements were collected pass by pass from the analysis, and the agreement was 9.08%. The agreement between the measured and analysed residual stress was 11%.


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## Body

## 1. Introduction

Fusion welding is one of the major joining techniques employed in industrial applications. In particular, gas tungsten arc welding (GTAW) allows yielding sound welds with different alloys. The selection of welding process parameters is one of the major challenging tasks to control welding residual stresses and distortions. Further, these welding process parameters will affect structural integrity. Experimental tests can be performed to estimate the improvement in parameters, but they are expensive and also quite time-consuming; in this scenario, welding numerical simulation may help avoid such drawbacks. Kermanpur et al. [1] developed an FEA model for multi-pass GTAW process of Incoloy 800 pipes. Temperature results obtained by using volumetric heat source were in good agreement with those obtained employing thermocouples located at the heat-affected zone of the joints. However, the authors did not focus on residual stresses caused by the joining process. In another recent work, Balram and Rajalakshmi [2] reported the experimental results regarding thermal stresses and thermal fields developed in the GTAW process applied to similar and dissimilar welded joints. The ERNiCrMo-3 alloy was used as filler wire. Tensile tests showed that the failure occurred within the parent metal, proving the high quality and strength of the welded joints obtained. Korrapati et al. [3] investigated the weldability and metallurgical and mechanical properties of the PCGTA welded Inconel 625 alloy employing ERNiCrMo-3 filler wire. In this case, despite the fact that defect-free welded joints were obtained, failures occurred at the weld region and the average tensile strength of the weldments was found to be 852.4 MPa.In order to decrease the computational time without losing accuracy, Perić et al. [4] proposed a T-joint numerical model conducted by combining the shell and 3D finite elements. Results of thermal and displacement distributions were found in good agreement with those measured in real joints. Finally, the influence of the 3D model size on the temperature, residual stress, and displacement distributions was investigated. Vemanaboina et al. [5] studied the residual stress evolutions in multi-pass dissimilar joints (IN 625-AISI 316L). The L4 orthogonal array was chosen for the tests. Two levels of each welding factor, filler wire and root gap parameters, were chosen for the experiments. It was concluded that the pulsed current-induced low residual stresses in the weld region were within the factor of safety of parent materials. In subsequent work [6], they deepened the weldability of such similar and dissimilar welded joints. Weldments free from defects and stresses within the yield limits of the base materials were obtained. In computational weld mechanics (CWM) [7, 8], the thermal load is obtained by using power density distribution functions that calibrate parameters using experimental results. This approach allows reducing the computational time required to calculate the residual stresses and distortions compared to that needed by models based on fluid dynamic analyses.Nine different welding sequences [9] were used to find the best conditions that minimized distortions and residual stresses in a T-weldment. The simulation was carried out by using ABAQUS numerical code. As expected, the best conditions were achieved when joining both sides in the same direction and at the same time. Kamble and Rao [10] developed a three-dimensional sequentially coupled thermomechanical model of 10 mm thick plate. The GMAW process was used for joining two 3Cr12 stainless steel plates. The thermal study was carried out at different time intervals. Thermally induced residual stress was predicted using ANSYS numerical code. In that work, the authors described the effect of process parameters on thermal and structural behaviour of the welded joints. Attarha and Sattari-Far described a thermal study of similar and dissimilar single-pass butt-welded joints [11]. A 3D numerical model was developed with ABAQUS®, and the Goldak heat source was used to simulate the thermal input of the process (GTAW). Excellent agreement was observed between numerical and experimental temperature values measured with k-type thermocouples located in the heat-affected zone (HAZ). Capriccioli and Frosi [12] carried out a computational analysis of the multi-pass welding process for dissimilar materials. The 316L stainless steel to IN625 welding simulation was carried out for both TIG and laser welding using ASNSYS®. The mechanical results were found very sensitive to the mesh shape, which had to be very fine and regular close to the fusion zones. In that work, an effort was made to reduce the CPU time that is the major objective to achieve when simulating a multi-pass welding process. Lostado et al. [13, 14] used finite element models to better understand heat behaviour and its impact on angular distortion and bead shape in GMAW butt weldments. The study employed genetic algorithms with multi-objective functions. The influence of heat input reveals growing angular distortion and weldment bead shape. The FEA models and experimental findings correlate well. Another work reported that the tensile residual is maximum at the fusion zone and also stated that the findings of the FEA were in agreement with the experimental results [15].Weld beads and related regions undergo plastic deformation during the welding process as a result of heating and cooling cycles, resulting in residual stress. Thermal and lattice spacing impact residual stresses in weldments, resulting in microstructure changes and thermomechanical stresses. With the help of FEA, it is possible to forecast the degree of heat effect in the weldment. Since no work has been published on the in situ thermal behaviour study during GTAW for Inconel 625 material, the authors believe that there is a lack of confirmation on simulations for the estimate of temperature profiles and residual stresses. Multipass welding of Inconel 625 with GTAW process conditions is the major focus in the present planned study. Welded components are analysed in 3D to determine their thermal and residual stresses. With the ANSYS® package, APDL code is used to do thermomechanical analysis. Infrared thermography is used to measure welding temperatures. X-ray diffraction is used to evaluate residual stresses in a weldment after it has cooled to ambient temperature for verification.


## 2. Finite Element Analysis

Figure1 shows an overview of the present numerical model. ANSYS package was used to develop the welding simulation. The plate has a square butt groove with no gaps between the two parts. According to the real butt-welded joint thickness, the FZ height was increased by 1.7 mm at each run, taking advantage of the activation-deactivation function of elements implemented in ANSYS code (Figure 2), roughly equal to that of weld bead measured by experiment. The thermal analysis was computed with the 8-node thermal element [16] SOLID70 and then switched to the 8-node finite element SOLID45 for the subsequent structural calculation. The two types of mesh options are used for the simulation models. The finer mesh is applied at fusion zone with a mesh size of 1.5 mm, and coarse mesh is applied to the rest of the plate with a mesh size of 3 mm, as shown in Figure 3. In this study, an equal time interval is assumed for every pass as heating time. The temperature-dependent [12] thermal and mechanical properties considered for Inconel 625 for the present study have been depicted in Figure 4.Figure 1
Overview of the thermo-elastic-plastic FEM analysis procedure.Figure 2
Simulation models for each pass. (a) Model for pass-1. (b) Model for pass-2. (c) Model for pass-3.
(a)(b)(c)Figure 3
Meshing of the model.Figure 4
Temperature-dependent material properties.
(a)(b)Goldak et al. proposed double ellipsoidal heat source model for the arc welding process [17]. For present weld simulations, the moving heat source model is treated as volumetric heat flux with constant heat input throughout the length. For each weld pass the bead size, initial boundary conditions are defined along with volumetric heat flux. The constant heat input loads are calculated as per the welding process parameters shown in Table 1.Table 1
Multi-pass welding process parameter.
Pass no.Welding current (I)Root gapArgon gas flow rateTime for each passAmmLPMsPass-114521236Pass-214527Pass-314531The volumetric heat flux [18, 19] of each weld pass is determined using the following equation:(1)Q=ηUIV,where η is the arc welding efficiency, U is the voltage, I is the welding current, and V is the volume of weld pass. The volume of the bead is added for each as shown in Figure 2. The value of arc efficiency is assumed to be 0.65 for the GTAW welding process. The heat conduction equation for welding simulation is given by(2)∂∂xk∂T∂x+∂∂yk∂T∂y+∂∂zk∂T∂z+Q=−ρCp∂T∂t,where ρ is the density, Cp is the specific heat under constant pressure, and k is the parent material conductivity. The coefficient of heat transfer rate was calculated for the weldment (equation (3)). Heat loss by convection was applied at the top and side faces of the weldment, while heat loss by both convection and radiation (equation (4)) was taken into account over the surface of the third weld bead obtained during the last welding run. In equations (4) and (5), T0 is the ambient temperature, εis the emissivity of the parent material, σ is the Stefan–Boltzmann constant, and h is the convective heat coefficient.(3)H=24.1∗10−4εT1.61,(4)qc=hT−T0,(5)qr=εσT4−T04.Boundary conditions were applied in order to simulate the thermal behaviour induced by the three passes.(1)
For pass-1, initial temperature was ambient temperature.(2)
Convention was applied at the root opening of the plates for pass-1 and pass-2.(3)
In pass-3, both convection and radiation were specified only on the top surface of the weld plate.(4)
The inter-pass [20] temperature is considered for pass-2 and pass-3 to avoid hot cracking. The initial temperature for pass-I is ambient, i.e., 30°C, and for pass-2 and pass-3, it was maintained at about 200–250°C.


## 3. Experimentation Procedure

The real butt-welded joint was produced by the GTAW technique. The dimensions of the plates were100 mm length × 60 mm width × 5 mm thickness, as shown in Figure5. The single V-groove angle of 60° was used. The gap between the plates was filled with three passes: pass-1 (root pass), pass-2 (filler pass), and pass-3 (cap pass). ERNiCrMo-3 was used as filler wire. Base material and filler wire chemical composition are given in Table 2. The base material mechanical properties are listed in Table 3. The process parameters chosen for experimentation are welding current (I), root gap (RG), and shielding gas flow rate (G) and are summarized in Table 1.Figure 5
Multi-pass welding process.Table 2
Base plate and filler material chemical properties (wt %).
SamplesNiCMnSCuSiCrPFeAlMoTiOthersInconel 625580.10.50.0150.50.520–230.01550.408–100.1—Filler wireERNiCrMo-3640.10.50.0150.500.522–230.01510.400.0150.40Nb 3.6–4.5,Table 3
Parent material mechanical properties.
MaterialYield strength (YS) (MPa)Poisson’s ratioCoefficient of thermal expansionInconel 6252540.2812.3e−6Welding current, root gap, and Argon flow rate were set to 145 A, 2 mm, and 15LPM, respectively. The same parameters are used for all passes. To avoid the hot cracking in the weld, an inter-pass temperature [21] (∼150–2500C) is maintained between the runs. Sound welded joints were obtained, and surface cracks and defects are verified by visual inspection and X-ray radiography.


### 3.1. Measuring Techniques

#### 3.1.1. Infrared Thermography

Infrared thermography and X-ray diffraction techniques are employed to measure thermal and residual stresses in the welded joints. The weld pool temperatures are recorded during each pass of the welding process with infrared thermography. The temperatures were measured using the FLIR infrared thermography, with an accuracy of ±0.1 C. The thermal imager measures the amount of heat emitted by the surface. The infrared thermography is used for measuring the temperature in the weldment. The base material surface-emission efficiency is necessary for measuring the surface temperature of the joint. In this work, the emissivity was taken equal toε = 0.9. Figure 6 shows how the infrared thermography works.Figure 6
Illustration of thermography system.


#### 3.1.2. X-Ray Diffraction

The weld area undergoes a heating and cooling cycle during the welding process. The thermal expansion and contraction of the parent material affect residual stresses and distortions. Figure7 displays the Bruker D8-DiscoverTM diffractometer for measuring residual stresses. Figure 8 shows the VantecTM area locator, and goniometer head is used for microfocus with laser tracking. Table 4 summarizes the measuring parameters.Figure 7
Bruker X-ray diffraction.Figure 8
Goniometer head with a detector.Table 4
XRD measuring parameters.
MeasurementTransverse directionTubeMn_K-AlphaBragg angle155.0°Peak locationGaussian-80%D-spacing (Angstroms)1.0771016Wavelength2.103The residual stresses were calculated by using Bragg’s law(equation (6)):(6)nλ=2dsinθ,where n refers to the order of reflection beam, d is the interplanar lattice spacing, λ is the wavelength of the incident wave, and θ is the scattering angle. In the transverse direction, the residual stresses are measured on the top surface and calculation [22] of the residual stress is carried out by using the following equation:(7)σϕ=md0E1+ν,where E is Young’s modulus, ν is Poisson’s coefficient, d0 is the stress-free lattice spacing, and m is the slope of the curve drawn between d (spacing) and sin2Ψ.


## 3.1. Measuring Techniques

### 3.1.1. Infrared Thermography

Infrared thermography and X-ray diffraction techniques are employed to measure thermal and residual stresses in the welded joints. The weld pool temperatures are recorded during each pass of the welding process with infrared thermography. The temperatures were measured using the FLIR infrared thermography, with an accuracy of ±0.1 C. The thermal imager measures the amount of heat emitted by the surface. The infrared thermography is used for measuring the temperature in the weldment. The base material surface-emission efficiency is necessary for measuring the surface temperature of the joint. In this work, the emissivity was taken equal toε = 0.9. Figure 6 shows how the infrared thermography works.Figure 6
Illustration of thermography system.


### 3.1.2. X-Ray Diffraction

The weld area undergoes a heating and cooling cycle during the welding process. The thermal expansion and contraction of the parent material affect residual stresses and distortions. Figure7 displays the Bruker D8-DiscoverTM diffractometer for measuring residual stresses. Figure 8 shows the VantecTM area locator, and goniometer head is used for microfocus with laser tracking. Table 4 summarizes the measuring parameters.Figure 7
Bruker X-ray diffraction.Figure 8
Goniometer head with a detector.Table 4
XRD measuring parameters.
MeasurementTransverse directionTubeMn_K-AlphaBragg angle155.0°Peak locationGaussian-80%D-spacing (Angstroms)1.0771016Wavelength2.103The residual stresses were calculated by using Bragg’s law(equation (6)):(6)nλ=2dsinθ,where n refers to the order of reflection beam, d is the interplanar lattice spacing, λ is the wavelength of the incident wave, and θ is the scattering angle. In the transverse direction, the residual stresses are measured on the top surface and calculation [22] of the residual stress is carried out by using the following equation:(7)σϕ=md0E1+ν,where E is Young’s modulus, ν is Poisson’s coefficient, d0 is the stress-free lattice spacing, and m is the slope of the curve drawn between d (spacing) and sin2Ψ.


## 3.1.1. Infrared Thermography

Infrared thermography and X-ray diffraction techniques are employed to measure thermal and residual stresses in the welded joints. The weld pool temperatures are recorded during each pass of the welding process with infrared thermography. The temperatures were measured using the FLIR infrared thermography, with an accuracy of ±0.1 C. The thermal imager measures the amount of heat emitted by the surface. The infrared thermography is used for measuring the temperature in the weldment. The base material surface-emission efficiency is necessary for measuring the surface temperature of the joint. In this work, the emissivity was taken equal toε = 0.9. Figure 6 shows how the infrared thermography works.Figure 6
Illustration of thermography system.


## 3.1.2. X-Ray Diffraction

The weld area undergoes a heating and cooling cycle during the welding process. The thermal expansion and contraction of the parent material affect residual stresses and distortions. Figure7 displays the Bruker D8-DiscoverTM diffractometer for measuring residual stresses. Figure 8 shows the VantecTM area locator, and goniometer head is used for microfocus with laser tracking. Table 4 summarizes the measuring parameters.Figure 7
Bruker X-ray diffraction.Figure 8
Goniometer head with a detector.Table 4
XRD measuring parameters.
MeasurementTransverse directionTubeMn_K-AlphaBragg angle155.0°Peak locationGaussian-80%D-spacing (Angstroms)1.0771016Wavelength2.103The residual stresses were calculated by using Bragg’s law(equation (6)):(6)nλ=2dsinθ,where n refers to the order of reflection beam, d is the interplanar lattice spacing, λ is the wavelength of the incident wave, and θ is the scattering angle. In the transverse direction, the residual stresses are measured on the top surface and calculation [22] of the residual stress is carried out by using the following equation:(7)σϕ=md0E1+ν,where E is Young’s modulus, ν is Poisson’s coefficient, d0 is the stress-free lattice spacing, and m is the slope of the curve drawn between d (spacing) and sin2Ψ.


## 4. Result and Discussion

ANSYS (APDL) was used for modelling, meshing, and transient thermal and static structural analysis. The computational welding mechanics technique was applied to reduce the CPU time by solving in a consecutive manner the thermal and the mechanical analysis for each welding pass. Temperatures and residual stresses at nodes were analysed in the transverse direction of the weldments. The details are illustrated in further sections given below.


### 4.1. Thermal Distribution

The welding cycle time was 40 s for all the passes. The cooling cycle was maintained for about 1000 s after the last welding run. Between a welding pass and the other one, an inter-pass temperature of about 250°C was maintained to avoid hot cracking. Figure9 illustrates the numerically assessed temperature map. During the first welding pass, a maximum temperature of 2080°C was observed, whereas the second pass induced a maximum temperature equal to 2158°C and a minimum temperature of 250°C (imposed inter-pass temperature). Finally, the pass-3 produced a maximum temperature of 1707°C. The maximum temperature was experimentally seen at the weld zone of the real joints. The heat is collected at the weld zone of the joint and extends in the transverse direction, which leads to form the HAZ. A narrow FZ was observed due to the low thermal conductivity of the analysed alloy.Figure 9
Distribution of temperatures in the weldment. (a) Weld pass-1. (b) Weld pass-2. (c) Weld pass-3.
(a)(b)(c)


### 4.2. Thermal Analysis Using Infrared Thermography

Thermal distribution during the welding is displayed in Figures10(a)–10(c). Line-1 represents the longitudinal and line-2 for the transverse direction of the weld plate, respectively, as shown in Figure 10(a). The temperatures can be recorded at any point of time, and the current thermography results are reported at the welding zone in the longitudinal and transverse directions at the instance of time. Figure 10(a) shows the temperature distribution ranges from 500°C to 1779.5°C in the transverse direction and from 500°C to 1580°C in the longitudinal direction. During the second welding pass, the measured maximum temperatures were 1838°C and 1867°C in the transverse and longitudinal directions, respectively (Figure 10(b)). The temperature distribution as shown in Figure 10(b) was waving up and down because the material was filled in the root gap, filler, and cap (Figure 5). The maximum interpass temperature 250°C was maintained in between the passes. Figure 10(c) shows the final welding pass; the maximum temperatures were reported to be 1325°C and 1878°C for the longitudinal and transverse directions, respectively. The measured torch temperature value was1000°C.Figure 10
Infrared thermography pass-wise analysis during the process. (a) Pass-1 IN625 to IN625. (b) Pass-2 IN625 to IN625. (c) Pass-3 IN625 to IN625.
(a)(b)(c)The experimental and numerical peak temperature values at each welding pass are compared in Figure11. It is observed that the thermal results of FEA simulation slightly differ from experimental ones. This phenomenon is due to the fixed time assumption for all the welding passes, i.e., 40 s.Figure 11
Comparison of thermal distribution.The FZ geometry and dimensions are shown in the macrograph of Figure12. It was wide, with 11.38 mm on the top of the weld, 5.69 mm in the midsection (2.5 mm thick), and 6.7 mm on the bottom of the plate. Metallographic examinations revealed a sound weld without defect and a fully penetrated bead. The filler wire is mixed well with parent material, and homogeneous joint was formed.Figure 12
Weld bead geometry of the final weldment.


### 4.3. Residual Stresses

The residual stress developed across the welding direction of various weldments using simulation is reported here. The residual stress distribution is shown in Figure13. After pass-1, the weldment experiences compressive stress of −200 MPa at fusion zone and −120 MPa at the end of the plate as shown in Figures 13(a). Figure 13(b) shows the residual stresses induced by pass-2. They range from −110 MPa in fusion zone to 120 MPa close to the HAZ. The parent metal is stress free. After pass-3, the total plate experiences tensile stresses, with a value of 178 MPa in the FZ and 18 MPa far from it (at the end of the plate) (Figure 13(c)).Figure 13
Distribution of residual stress using FEA. (a) Weld pass-1. (b) Weld pass-2. (c) Weld pass-3.
(a)(b)(c)The measured tensile residual stress distribution was observed at weld zone and compressive stress in remaining zones. This is due to the expansion of the material during welding and high temperatures at the fusion zone; however, this expansion is retarded by the neighbouring base metal region. The material experiences contraction while cooling to maintain the plate’s original dimension, which generates plastic deformation. At HAZ, it undergoes high-stress concentration to maintain the equilibrium between shrinkage action of the base plate and the solidification of the molten weld pool. It is determined that balanced stress distribution in the weldment is due to uniform thermal conductivity along the plates. Figure14 shows the comparison between experimentally measured and numerically predicted residual stresses analysed for a welded joint. It is observed that the material experiences tensile stresses near the weld bead. The maximum experimental and numerical tensile stress was observed to be 200 MPa and 178 MPa, respectively. Further, it was verified that the stresses were not self-balanced in the structure. Temperature measurements were collected pass by pass from the analysis, and the agreement was 9.08%. The agreement between the measured and analysed residual stress was 11%. Due to the influence of heat input in small areas during establishing the weld joint, the regions next to the weld line undergo severe thermal cycles, resulting in an increase in residual stresses. The result will be a reduction in the structure’s life. The same was seen in the current investigation for welding simulation results, with an increase in the error percent of residual stresses. Studies have shown that the maximum residual stress occurs due to the assumption of a constant welding duration in the simulation. In the experiment, the welding duration is changed depending on the weld machine’s duty cycle and when the filler wire melts and solidifies. Additionally, in Lostado et al.’s research [15], they noted that the welded joints can be expanded greatly if nonlinearities are present. This influence results in the dropping of structural integrity.Figure 14
Comparison of residual stresses.


## 4.1. Thermal Distribution

The welding cycle time was 40 s for all the passes. The cooling cycle was maintained for about 1000 s after the last welding run. Between a welding pass and the other one, an inter-pass temperature of about 250°C was maintained to avoid hot cracking. Figure9 illustrates the numerically assessed temperature map. During the first welding pass, a maximum temperature of 2080°C was observed, whereas the second pass induced a maximum temperature equal to 2158°C and a minimum temperature of 250°C (imposed inter-pass temperature). Finally, the pass-3 produced a maximum temperature of 1707°C. The maximum temperature was experimentally seen at the weld zone of the real joints. The heat is collected at the weld zone of the joint and extends in the transverse direction, which leads to form the HAZ. A narrow FZ was observed due to the low thermal conductivity of the analysed alloy.Figure 9
Distribution of temperatures in the weldment. (a) Weld pass-1. (b) Weld pass-2. (c) Weld pass-3.
(a)(b)(c)


## 4.2. Thermal Analysis Using Infrared Thermography

Thermal distribution during the welding is displayed in Figures10(a)–10(c). Line-1 represents the longitudinal and line-2 for the transverse direction of the weld plate, respectively, as shown in Figure 10(a). The temperatures can be recorded at any point of time, and the current thermography results are reported at the welding zone in the longitudinal and transverse directions at the instance of time. Figure 10(a) shows the temperature distribution ranges from 500°C to 1779.5°C in the transverse direction and from 500°C to 1580°C in the longitudinal direction. During the second welding pass, the measured maximum temperatures were 1838°C and 1867°C in the transverse and longitudinal directions, respectively (Figure 10(b)). The temperature distribution as shown in Figure 10(b) was waving up and down because the material was filled in the root gap, filler, and cap (Figure 5). The maximum interpass temperature 250°C was maintained in between the passes. Figure 10(c) shows the final welding pass; the maximum temperatures were reported to be 1325°C and 1878°C for the longitudinal and transverse directions, respectively. The measured torch temperature value was1000°C.Figure 10
Infrared thermography pass-wise analysis during the process. (a) Pass-1 IN625 to IN625. (b) Pass-2 IN625 to IN625. (c) Pass-3 IN625 to IN625.
(a)(b)(c)The experimental and numerical peak temperature values at each welding pass are compared in Figure11. It is observed that the thermal results of FEA simulation slightly differ from experimental ones. This phenomenon is due to the fixed time assumption for all the welding passes, i.e., 40 s.Figure 11
Comparison of thermal distribution.The FZ geometry and dimensions are shown in the macrograph of Figure12. It was wide, with 11.38 mm on the top of the weld, 5.69 mm in the midsection (2.5 mm thick), and 6.7 mm on the bottom of the plate. Metallographic examinations revealed a sound weld without defect and a fully penetrated bead. The filler wire is mixed well with parent material, and homogeneous joint was formed.Figure 12
Weld bead geometry of the final weldment.


## 4.3. Residual Stresses

The residual stress developed across the welding direction of various weldments using simulation is reported here. The residual stress distribution is shown in Figure13. After pass-1, the weldment experiences compressive stress of −200 MPa at fusion zone and −120 MPa at the end of the plate as shown in Figures 13(a). Figure 13(b) shows the residual stresses induced by pass-2. They range from −110 MPa in fusion zone to 120 MPa close to the HAZ. The parent metal is stress free. After pass-3, the total plate experiences tensile stresses, with a value of 178 MPa in the FZ and 18 MPa far from it (at the end of the plate) (Figure 13(c)).Figure 13
Distribution of residual stress using FEA. (a) Weld pass-1. (b) Weld pass-2. (c) Weld pass-3.
(a)(b)(c)The measured tensile residual stress distribution was observed at weld zone and compressive stress in remaining zones. This is due to the expansion of the material during welding and high temperatures at the fusion zone; however, this expansion is retarded by the neighbouring base metal region. The material experiences contraction while cooling to maintain the plate’s original dimension, which generates plastic deformation. At HAZ, it undergoes high-stress concentration to maintain the equilibrium between shrinkage action of the base plate and the solidification of the molten weld pool. It is determined that balanced stress distribution in the weldment is due to uniform thermal conductivity along the plates. Figure14 shows the comparison between experimentally measured and numerically predicted residual stresses analysed for a welded joint. It is observed that the material experiences tensile stresses near the weld bead. The maximum experimental and numerical tensile stress was observed to be 200 MPa and 178 MPa, respectively. Further, it was verified that the stresses were not self-balanced in the structure. Temperature measurements were collected pass by pass from the analysis, and the agreement was 9.08%. The agreement between the measured and analysed residual stress was 11%. Due to the influence of heat input in small areas during establishing the weld joint, the regions next to the weld line undergo severe thermal cycles, resulting in an increase in residual stresses. The result will be a reduction in the structure’s life. The same was seen in the current investigation for welding simulation results, with an increase in the error percent of residual stresses. Studies have shown that the maximum residual stress occurs due to the assumption of a constant welding duration in the simulation. In the experiment, the welding duration is changed depending on the weld machine’s duty cycle and when the filler wire melts and solidifies. Additionally, in Lostado et al.’s research [15], they noted that the welded joints can be expanded greatly if nonlinearities are present. This influence results in the dropping of structural integrity.Figure 14
Comparison of residual stresses.


## 5. Conclusions

Computational welding mechanics used ANSYS to predict residual stresses and temperature distribution arising from the Inconel 625 multi-pass GTAW process. A double ellipsoidal volumetric heat source model with boundary conditions was used for the thermal analysis.(i)
The multi-pass welding process was established successfully for Inconel 625 by the GTAW process for 5 mm thick plate free from flaws and defects.(ii)
The hot cracking flaws were eliminated by including inter-pass temperatures between the second and third passes. The results are in good agreement with the predicted thermal and mechanical boundary conditions.(iii)
The residual stresses generated were within the yield limits of the parent material.(iv)
The factor of safety was 1.27 for experimentation and 1.42 for simulation of the Inconel 625 welding process.(v)
Temperature measurements were collected pass by pass from the analysis, and the agreement was 9.08%. The agreement between the measured and analysed residual stress was 11%.



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