Numerical Simulation of Residual Stress and Deformation in Wire Arc Additive Manufacturing

In this paper, multi-layer and multi-pass arc additive manufacturing experiments were carried out on the Q345 substrate using Y309L welding wire. Based on MSC. Marc software, a thermal-elastic-plastic finite element method was developed to numerically simulate the temperature field, stress field, and deformation during the additive manufacturing process. The effects of the substrate thickness and interpass temperature on the temperature field, stress field, and deformation were discussed. The results indicated that the deposition materials at different positions experienced different thermal cycles, which might lead to the non-uniform microstructure and mechanical properties within the workpiece. The interpass temperature and the thickness of the substrate influenced the residual stress distribution in the additive manufactured structure. A low interpass temperature and thin substrate was able to effectively reduce the tensile residual stress. The thick substrate resulted in a small angular deformation of the substrate during the additive manufacturing process.


Introduction
Wire Arc Additive Manufacturing (WAAM) is an additive manufacturing technology that uses an arc as a heat source to melt wires for directional deposition. Compared with other additive manufacturing technologies, WAAM technology has outstanding advantages, such as a high efficiency and low cost. During the manufacturing process, the wire metal cladding amount can reach 10 kg/h, and the material utilization rate is higher than 90% [1,2]. The prices of the wire and the equipment are significantly lower than in other additive methods, such as selective laser melting (SLM) [3] and electron beam additive manufacturing (EBAM) [4]. Large-sized or complex-structure parts can be manufactured using WAAM technology [5,6]. Meanwhile, WAAM products show a high performance and can even be comparable to traditional forgings under certain specific process conditions [7]. Thus, compared with traditional manufacturing methods, WAAM provides a new high-quality, high-efficiency, and low-cost method for the production of small-batch customized structural parts. At present, WAAM technology is widely used in practical industries. The Cranfield University in the UK has cooperated with the European Space Agency to manufacture large titanium alloy parts for aircraft using WAAM technology [8,9], and Bombardier Inc. has used WAAM technology to manufacture the rib of a wing [10]-which greatly improved the utilization rate of the materials and greatly reduced their production costs.
There are mainly two hindrances that have limited the potential application of additive manufacturing technologies, including WAAM [11], SLM [12], and EBAM [13] technologies. The first is the material defects in the products, such as gas inclusions, key-hole porosity, and lack-of-fusion defects. The second is the excessive residual stress and deformation caused by the rapid repeated heating and cooling process [14][15][16]. The existence of residual stress and deformation will not only greatly reduce the fatigue strength, crack resistance,

Experimental Procedures
In the additive manufacturing experiment, the substrate was Q345 low-alloy highstrength steel, and the deposition material was Y309L stainless steel wire with a diameter of 1.2 mm. Their chemical compositions are shown in Table 1. The substrate dimensions and weld pass arrangement are shown in Figure 1. The additive manufacturing experiments were carried out using robotic MIG (Metal-Inert Gas) welding machine TM1800 made by Panasonic (Tangshan, China). There were 4 layers and 10 passes in total. The welding current was 185 A, the welding voltage was 20 V, and the welding speed was 300 mm/min. The protective gas was pure Ar, and the gas flow was 18 L/min. After each welding pass, the workpiece was cooled to room temperature naturally in the air before the next welding pass. During the additive manufacturing process, no external restraint was applied and the angular deformation of the substrate was measured after each pass. After the additive manufacturing was completed, the deformation of the edge line L1 of the substrate (shown  Figure 1a) was recorded using the contour method. A schematic diagram of the substrate deformation measurement is shown in Figure 2. Due to the uneven surface of the additive manufactured workpiece, it is difficult to accurately measure the surface residual stress by the slicing method, pinhole method, or X-ray method. Therefore, the residual stress of the additive manufactured workpiece was not measured in this study. In future research, we plan to measure the residual stress of the additive manufactured products using the neutron diffraction method or the synchrotron radiation method. welding pass, the workpiece was cooled to room temperature naturally in the air before the next welding pass. During the additive manufacturing process, no external restraint was applied and the angular deformation of the substrate was measured after each pass. After the additive manufacturing was completed, the deformation of the edge line L1 of the substrate (shown in Figure 1a) was recorded using the contour method. A schematic diagram of the substrate deformation measurement is shown in Figure 2. Due to the uneven surface of the additive manufactured workpiece, it is difficult to accurately measure the surface residual stress by the slicing method, pinhole method, or X-ray method. Therefore, the residual stress of the additive manufactured workpiece was not measured in this study. In future research, we plan to measure the residual stress of the additive manufactured products using the neutron diffraction method or the synchrotron radiation method.

Numerical Simulation
According to the geometric dimensions of the workpiece, the corresponding finite element model was established, as shown in Figure 3. It should be noted here that when simulating the deposition process of additive manufacturing, to simplify the modeling process and improve the calculation efficiency, this model did not accurately consider the cross-sectional shape of each weld bead and weld formation. In the established model, the center position and cross-sectional area of the weld were roughly equivalent to the actual weld bead. The height width of each weld pass were about 3.5 mm and 7.0 mm, respectively. To balance computational accuracy and computational efficiency, fine meshes were used in the weld pass and the heat-affected zone of the substrate, while relatively sparse meshes were used in the rest zone. The total number of elements in the model was 27,000 and the total number of nodes was 31,720.
A thermal-elastic-plastic finite element method was developed to numerically simulate the temperature field, stress field, and deformation during the additive manufacturing process, which was described in this section. The calculation process consisted of two parts, which were the thermal analysis and mechanical analysis. During the thermal analysis process, the temperature field was obtained. Then, the temperature data were introduced into the mechanical analysis as a thermal load to compute the stress and deformation. A heat source model was established. In this model, the actual additive welding pass, the workpiece was cooled to room temperature naturally in the air before the next welding pass. During the additive manufacturing process, no external restraint was applied and the angular deformation of the substrate was measured after each pass. After the additive manufacturing was completed, the deformation of the edge line L1 of the substrate (shown in Figure 1a) was recorded using the contour method. A schematic diagram of the substrate deformation measurement is shown in Figure 2. Due to the uneven surface of the additive manufactured workpiece, it is difficult to accurately measure the surface residual stress by the slicing method, pinhole method, or X-ray method. Therefore, the residual stress of the additive manufactured workpiece was not measured in this study. In future research, we plan to measure the residual stress of the additive manufactured products using the neutron diffraction method or the synchrotron radiation method.

Numerical Simulation
According to the geometric dimensions of the workpiece, the corresponding finite element model was established, as shown in Figure 3. It should be noted here that when simulating the deposition process of additive manufacturing, to simplify the modeling process and improve the calculation efficiency, this model did not accurately consider the cross-sectional shape of each weld bead and weld formation. In the established model, the center position and cross-sectional area of the weld were roughly equivalent to the actual weld bead. The height width of each weld pass were about 3.5 mm and 7.0 mm, respectively. To balance computational accuracy and computational efficiency, fine meshes were used in the weld pass and the heat-affected zone of the substrate, while relatively sparse meshes were used in the rest zone. The total number of elements in the model was 27,000 and the total number of nodes was 31,720.
A thermal-elastic-plastic finite element method was developed to numerically simulate the temperature field, stress field, and deformation during the additive manufacturing process, which was described in this section. The calculation process consisted of two parts, which were the thermal analysis and mechanical analysis. During the thermal analysis process, the temperature field was obtained. Then, the temperature data were introduced into the mechanical analysis as a thermal load to compute the stress and deformation. A heat source model was established. In this model, the actual additive

Numerical Simulation
According to the geometric dimensions of the workpiece, the corresponding finite element model was established, as shown in Figure 3. It should be noted here that when simulating the deposition process of additive manufacturing, to simplify the modeling process and improve the calculation efficiency, this model did not accurately consider the cross-sectional shape of each weld bead and weld formation. In the established model, the center position and cross-sectional area of the weld were roughly equivalent to the actual weld bead. The height width of each weld pass were about 3.5 mm and 7.0 mm, respectively. To balance computational accuracy and computational efficiency, fine meshes were used in the weld pass and the heat-affected zone of the substrate, while relatively sparse meshes were used in the rest zone. The total number of elements in the model was 27,000 and the total number of nodes was 31,720.
A thermal-elastic-plastic finite element method was developed to numerically simulate the temperature field, stress field, and deformation during the additive manufacturing process, which was described in this section. The calculation process consisted of two parts, which were the thermal analysis and mechanical analysis. During the thermal analysis process, the temperature field was obtained. Then, the temperature data were introduced into the mechanical analysis as a thermal load to compute the stress and deformation. A heat source model was established. In this model, the actual additive manufacturing process was considered and the parameters related to heat transfer were set to improve the calculation accuracy of the temperature field. During the mechanical analysis, irrelevant factors were eliminated to shorten the calculation time. manufacturing process was considered and the parameters related to heat transfer were set to improve the calculation accuracy of the temperature field. During the mechanical analysis, irrelevant factors were eliminated to shorten the calculation time. The calculation software used in this study was MSC. MARC (2021, MSC software, Irvine, CA, USA). The element used in this model was the hexahedral 8-node element [26]. Since no external constraints were applied during the experiment, three-point constraints were applied in the finite element model to prevent the model from rigid movements during the calculation. The life-death element was used to simulate the deposition process of the metal. There were four calculation cases in this study, as shown in Table 2. Case A was consistent with the experiment. After each welding pass, the workpiece was cooled to room temperature before the next welding pass. The interpass temperature in Case A was 20 °C. In Case B, Case C, and Case D, the thickness of the substrate was varied to discuss its effects on the temperature field, stress field, and deformation of workpiece. To increase the efficiency of the additive manufacturing, the time between deposition layers was shortened to 33 s [15,27,28]. Thus, the interpass temperatures in Case B, Case C, and Case D were higher than 20 °C.

Heat Source Model and Thermal Analysis
In the additive manufacturing process, the heat transfer equation of the arc heat in the material is as shown in Equation (1).
where T is the temperature, λ is the thermal conductivity of materials, qv is the heat source power, ρ is the material density, c is the specific heat capacity of the materials, and t is the heat transfer time. x, y, and z are coordinates in the space coordinate system. The calculation software used in this study was MSC. MARC (2021, MSC software, Irvine, CA, USA). The element used in this model was the hexahedral 8-node element [26]. Since no external constraints were applied during the experiment, three-point constraints were applied in the finite element model to prevent the model from rigid movements during the calculation. The life-death element was used to simulate the deposition process of the metal. There were four calculation cases in this study, as shown in Table 2. Case A was consistent with the experiment. After each welding pass, the workpiece was cooled to room temperature before the next welding pass. The interpass temperature in Case A was 20 • C. In Case B, Case C, and Case D, the thickness of the substrate was varied to discuss its effects on the temperature field, stress field, and deformation of workpiece. To increase the efficiency of the additive manufacturing, the time between deposition layers was shortened to 33 s [15,27,28]. Thus, the interpass temperatures in Case B, Case C, and Case D were higher than 20 • C.

Heat Source Model and Thermal Analysis
In the additive manufacturing process, the heat transfer equation of the arc heat in the material is as shown in Equation (1).
where T is the temperature, λ is the thermal conductivity of materials, q v is the heat source power, ρ is the material density, c is the specific heat capacity of the materials, and t is the heat transfer time. x, y, and z are coordinates in the space coordinate system. The dual ellipsoid heat source model proposed by Goldak et al. [29] was used to simulate the heat input in the additive manufacturing process. The heat flux densities of its front and back halves are described by Equations (2) and (3), respectively.
where q f and q r are the heat flux densities in the front and back half of the double ellipsoid heat source model, respectively. Q is the welding heat (Q = ηUI, U is the voltage, I is the current, and η is the thermal efficiency 0.8 [30][31][32]). a f , a r , b, and c represent the shape parameters of the double ellipsoid, f f and f r represent the heat distribution function before and after the double ellipsoid; f f + f r = 2, and in this study, f f = 0.6, f r = 1.4 [33]. The convection and radiation were considered in this model to analyze the heat exchange between the workpiece and the external environment. The convective heat transfer is described by Newton's law (Equation (4)), and the radiation heat transfer is described by the Stefan-Boltzmann law (Equation (5)).
The changes in the material properties with temperature were considered in the calculation process. The high-temperature thermophysical properties of the Q345 steel substrate and the Y309L wire [31,32] are shown in Figure 4. The dual ellipsoid heat source model proposed by Goldak et al. [29] was used to simulate the heat input in the additive manufacturing process. The heat flux densities of its front and back halves are described by Equations (2) and (3), respectively.
where qf and qr are the heat flux densities in the front and back half of the double ellipsoid heat source model, respectively. Q is the welding heat (Q = ηUI, U is the voltage, I is the current, and η is the thermal efficiency 0.8 [30][31][32]). af, ar, b, and c represent the shape parameters of the double ellipsoid, ff and fr represent the heat distribution function before and after the double ellipsoid; ff + fr = 2, and in this study, ff = 0.6, fr = 1.4 [33]. The convection and radiation were considered in this model to analyze the heat exchange between the workpiece and the external environment. The convective heat transfer is described by Newton's law (Equation (4)), and the radiation heat transfer is described by the Stefan-Boltzmann law (Equation (5)).
The changes in the material properties with temperature were considered in the calculation process. The high-temperature thermophysical properties of the Q345 steel substrate and the Y309L wire [31,32] are shown in Figure 4.

Mechanical Analysis
When calculating the stress field and deformation, the model used was the same as when calculating the temperature field. The calculation results of the temperature field were loaded into the finite element model as thermal loads for the elastic-plastic analysis. The total strain of the material during the calculation process could be expressed by the following formula: where εtotal represents the total strain, εe is the elastic strain, εp is the plastic strain, εth is the thermal strain, εcr is the creep strain, and εph is the phase transformation strain.

Mechanical Analysis
When calculating the stress field and deformation, the model used was the same as when calculating the temperature field. The calculation results of the temperature field were loaded into the finite element model as thermal loads for the elastic-plastic analysis. The total strain of the material during the calculation process could be expressed by the following formula: where ε total represents the total strain, ε e is the elastic strain, ε p is the plastic strain, ε th is the thermal strain, ε cr is the creep strain, and ε ph is the phase transformation strain. The solid-state transformation of Q345 steel has little effect on residual stress and deformation [32]. The deposited material in this study was Y309L austenitic stainless steel, which had no solid-state transformation during the welding. Thus, the transformation strain was not considered in the calculation process. Since the high-temperature residence time in the arc additive manufacturing process was short and the creep phenomenon was not obvious, the creep strain was ignored. The total strain of the material during the additive manufacturing process could be expressed by the following formula: The elastic strain calculation follows Hook's law, and the plastic deformation adopts the Von-Mises criterion. The work hardening phenomenon of Q345 was not obvious [36]. However, Y309L is austenitic stainless steel with a significant tendency for work hardening. Thus, the work-hardening phenomenon of Q345 was ignored in the calculation process, and the isotropic criterion was used to describe the work-hardening effect of the Y309L [37]. At the same time, the annealing softening effect of the Y309L stainless steel was considered because the deposition layers underwent multiple thermal cycles. In this study, a step annealing model was used to describe the annealing softening effect. The annealing temperature was set to 1000 • C [38]. The high-temperature mechanical properties of the Q345 and the Y309L are shown in Figure 5. The solid-state transformation of Q345 steel has little effect on residual stress and deformation [32]. The deposited material in this study was Y309L austenitic stainless steel, which had no solid-state transformation during the welding. Thus, the transformation strain was not considered in the calculation process. Since the high-temperature residence time in the arc additive manufacturing process was short and the creep phenomenon was not obvious, the creep strain was ignored. The total strain of the material during the additive manufacturing process could be expressed by the following formula: The elastic strain calculation follows Hook's law, and the plastic deformation adopts the Von-Mises criterion. The work hardening phenomenon of Q345 was not obvious [36]. However, Y309L is austenitic stainless steel with a significant tendency for work hardening. Thus, the work-hardening phenomenon of Q345 was ignored in the calculation process, and the isotropic criterion was used to describe the work-hardening effect of the Y309L [37]. At the same time, the annealing softening effect of the Y309L stainless steel was considered because the deposition layers underwent multiple thermal cycles. In this study, a step annealing model was used to describe the annealing softening effect. The annealing temperature was set to 1000 °C [38]. The high-temperature mechanical properties of the Q345 and the Y309L are shown in Figure 5.  Figure 6 shows the calculated and experimental angular deformations of the substrate in Case A. The calculated results agreed well with the experimental measurements, which verified the reliability of the developed finite element method. When the additive manufacturing was finished, obvious asymmetric welding deformation occurred in the substrate. The final angular deformation of the substrate was about 8°. The angular deformation increment was significant when the first layer was deposited. Then, the angular deformation increments gradually decreased with increases in the deposition height.  Figure 6 shows the calculated and experimental angular deformations of the substrate in Case A. The calculated results agreed well with the experimental measurements, which verified the reliability of the developed finite element method. When the additive manufacturing was finished, obvious asymmetric welding deformation occurred in the substrate. The final angular deformation of the substrate was about 8 • . The angular deformation increment was significant when the first layer was deposited. Then, the angular deformation increments gradually decreased with increases in the deposition height. Figure 7 shows the temperature distributions in Case C when the heat source moved to the center of the 1st, 6th, and 10th weld pass. It can be seen from Figure 7 that as the additive manufacturing process proceeded, the high-temperature area of the substrate and the size of the molten pool increased accordingly. This phenomenon was mainly due to the heat-accumulation effect of the additive manufacturing process. During the additive manufacturing process, more and more heat accumulated in the workpiece, increasing the temperature of the substrate and the size of the molten pool.  Figure 7 shows the temperature distributions in Case C when the heat source moved to the center of the 1st, 6th, and 10th weld pass. It can be seen from Figure 7 that as the additive manufacturing process proceeded, the high-temperature area of the substrate and the size of the molten pool increased accordingly. This phenomenon was mainly due to the heat-accumulation effect of the additive manufacturing process. During the additive manufacturing process, more and more heat accumulated in the workpiece, increasing the temperature of the substrate and the size of the molten pool.  Figure 8 illustrates the temperature histories of the deposition materials in the 1st, 6th, and 10th weld passes. Due to the heating effect of the subsequent weld passes, these thermal cures showed different characteristics. For the deposition material in the 1st weld pass, there were a total of ten temperature peaks in its thermal curve. The first temperature peak (1857 °C) was due to the deposition process of the 1st weld pass. The other nine temperature peaks were due to the heating effect of subsequent weld passes. The closer the subsequent weld pass was to the 1st weld pass, the more significant heating effect on the deposition materials in the 1st weld pass it had, and the higher the corresponding temperature peak was. Since the 5th weld pass was near the 1st weld pass, it had a significant heating effect on the deposition materials in the 1st weld pass. The corresponding peak temperature exceeded the melting point of the material, resulting in remelting of the deposition materials in the 1st weld pass. For the deposition materials in the 6th and 10th weld pass, their thermal curves were different from that of the 1st weld pass. Owing to   Figure 7 shows the temperature distributions in Case C when the heat source moved to the center of the 1st, 6th, and 10th weld pass. It can be seen from Figure 7 that as the additive manufacturing process proceeded, the high-temperature area of the substrate and the size of the molten pool increased accordingly. This phenomenon was mainly due to the heat-accumulation effect of the additive manufacturing process. During the additive manufacturing process, more and more heat accumulated in the workpiece, increasing the temperature of the substrate and the size of the molten pool.  Figure 8 illustrates the temperature histories of the deposition materials in the 1st, 6th, and 10th weld passes. Due to the heating effect of the subsequent weld passes, these thermal cures showed different characteristics. For the deposition material in the 1st weld pass, there were a total of ten temperature peaks in its thermal curve. The first temperature peak (1857 °C) was due to the deposition process of the 1st weld pass. The other nine temperature peaks were due to the heating effect of subsequent weld passes. The closer the subsequent weld pass was to the 1st weld pass, the more significant heating effect on the deposition materials in the 1st weld pass it had, and the higher the corresponding temperature peak was. Since the 5th weld pass was near the 1st weld pass, it had a significant heating effect on the deposition materials in the 1st weld pass. The corresponding peak temperature exceeded the melting point of the material, resulting in remelting of the deposition materials in the 1st weld pass. For the deposition materials in the 6th and 10th weld pass, their thermal curves were different from that of the 1st weld pass. Owing to  Figure 8 illustrates the temperature histories of the deposition materials in the 1st, 6th, and 10th weld passes. Due to the heating effect of the subsequent weld passes, these thermal cures showed different characteristics. For the deposition material in the 1st weld pass, there were a total of ten temperature peaks in its thermal curve. The first temperature peak (1857 • C) was due to the deposition process of the 1st weld pass. The other nine temperature peaks were due to the heating effect of subsequent weld passes. The closer the subsequent weld pass was to the 1st weld pass, the more significant heating effect on the deposition materials in the 1st weld pass it had, and the higher the corresponding temperature peak was. Since the 5th weld pass was near the 1st weld pass, it had a significant heating effect on the deposition materials in the 1st weld pass. The corresponding peak temperature exceeded the melting point of the material, resulting in remelting of the deposition materials in the 1st weld pass. For the deposition materials in the 6th and 10th weld pass, their thermal curves were different from that of the 1st weld pass. Owing to the heat-accumulation effect of the additive manufacturing process, the maximum peak temperatures of the 1st, 6th, and 10th weld passes gradually increased, reaching 1857 • C, 2056 • C, and 2180 • C, respectively. In the thermal curve of the deposition materials in the 6th pass, the corresponding peak temperatures of the 7th, 8th, and 9th weld passes were close to the melting point of the deposition material. It can be seen from the above analysis that the deposition materials at different positions experienced different thermal cycles, which may have led to the non-uniform microstructure and mechanical properties within the workpiece.

Temperature Field
temperatures of the 1st, 6th, and 10th weld passes gradually increased, reaching 1857 °C, 2056 °C, and 2180 °C, respectively. In the thermal curve of the deposition materials in the 6th pass, the corresponding peak temperatures of the 7th, 8th, and 9th weld passes were close to the melting point of the deposition material. It can be seen from the above analysis that the deposition materials at different positions experienced different thermal cycles, which may have led to the non-uniform microstructure and mechanical properties within the workpiece.  Figure 9 shows the temperature cycling curves at point A when the substrate thicknesses were 5 mm, 10 mm, and 20 mm, respectively. Point A was located in the middle of the substrate, 5 mm from the edge of the 1st weld pass. It could be seen from the figure that as the additive manufacturing process proceeded, the interpass temperature increased. With the same welding parameters, a thick substrate can effectively reduce the interpass temperature. When the thickness of the substrate increased from 5 mm to 20 mm, the maximum temperature at point A decreased from 642 °C to 304 °C. This was because, during the additive manufacturing process, the thermal conduction and heat dissipation of the deposition heat through the substrate was much faster than the convection and radiation heat dissipation on the surface of the deposition layer. The thicker the substrate was, the more conducive to rapid heat dissipation it was.   Figure 9 shows the temperature cycling curves at point A when the substrate thicknesses were 5 mm, 10 mm, and 20 mm, respectively. Point A was located in the middle of the substrate, 5 mm from the edge of the 1st weld pass. It could be seen from the figure that as the additive manufacturing process proceeded, the interpass temperature increased. With the same welding parameters, a thick substrate can effectively reduce the interpass temperature. When the thickness of the substrate increased from 5 mm to 20 mm, the maximum temperature at point A decreased from 642 • C to 304 • C. This was because, during the additive manufacturing process, the thermal conduction and heat dissipation of the deposition heat through the substrate was much faster than the convection and radiation heat dissipation on the surface of the deposition layer. The thicker the substrate was, the more conducive to rapid heat dissipation it was.
2056 °C, and 2180 °C, respectively. In the thermal curve of the deposition materials in the 6th pass, the corresponding peak temperatures of the 7th, 8th, and 9th weld passes were close to the melting point of the deposition material. It can be seen from the above analysis that the deposition materials at different positions experienced different thermal cycles, which may have led to the non-uniform microstructure and mechanical properties within the workpiece.  Figure 9 shows the temperature cycling curves at point A when the substrate thicknesses were 5 mm, 10 mm, and 20 mm, respectively. Point A was located in the middle of the substrate, 5 mm from the edge of the 1st weld pass. It could be seen from the figure that as the additive manufacturing process proceeded, the interpass temperature increased. With the same welding parameters, a thick substrate can effectively reduce the interpass temperature. When the thickness of the substrate increased from 5 mm to 20 mm, the maximum temperature at point A decreased from 642 °C to 304 °C. This was because, during the additive manufacturing process, the thermal conduction and heat dissipation of the deposition heat through the substrate was much faster than the convection and radiation heat dissipation on the surface of the deposition layer. The thicker the substrate was, the more conducive to rapid heat dissipation it was.   Figure 10 shows the residual stress distribution on the central sections of the models in four cases. High residual stress formed inside the deposition layers as well as in the middle of the substrate. The longitudinal and transverse residual stress peaks inside the deposition layers exceeded the room-temperature yield strength of Y309L. This was because Y309L had a high tendency for work hardening. During the additive manufacturing process, large plastic deformation formed in the deposition layers, increasing the yield strength of the material. In addition, the materials at certain locations inside the deposited layers were in a state of triaxial stress, which also contributed to the formation of high residual stresses. increased gradually. The triaxial residual stresses limited the further plastic deformation of the materials at the weld toes and increased the risk of brittle fractures. Comparing Case A and Case C, it could be found that the longitudinal high tensile stress area in Case C was significantly larger than that in Case A, while the transverse compressive residual stress area was smaller than that in Case A. Thus, a low interpass temperature could effectively reduce the tensile residual stress during the additive manufacturing process.  Figure 11 shows the distribution of longitudinal and transverse residual stress on the central section of the substrate along line L2, which was 2 mm away from the upper surface of the substrate. The longitudinal residual stress was high tensile stress in the middle of the substrate and was compressive stress on both sides of the substrate. In Case B, Case C, and Case D, the longitudinal tensile stress peaks were located below the weld toes. With the increase in substrate thickness, the longitudinal tensile stress peaks (391 MPa, 383 MPa, 337 MPa) decreased gradually. The transverse tensile stress peaks appeared below the weld toes. In the area between the two weld toes, the transverse tensile stress In Case B, Case C, and Case D, high longitudinal tensile residual stress formed inside the deposition layers and in the middle of the substrates. With increases in the substrate thickness, the longitudinal high tensile stress area in the deposition layers gradually increased, while the longitudinal high tensile stress area in the middle of the substrate gradually decreased. The transverse tensile residual stress was mainly concentrated in the vicinity of the upper and lower surfaces of the substrate, and the balanced transverse compressive residual stress was distributed in the middle of the substrate and the top of the deposition layers. At the weld toes, there were high tensile residual stresses in three directions. With the increase of the substrate thickness, the area of high tensile residual stress increased gradually. The triaxial residual stresses limited the further plastic deformation of the materials at the weld toes and increased the risk of brittle fractures. Comparing Case A and Case C, it could be found that the longitudinal high tensile stress area in Case C was significantly larger than that in Case A, while the transverse compressive residual stress area was smaller than that in Case A. Thus, a low interpass temperature could effectively reduce the tensile residual stress during the additive manufacturing process. Figure 11 shows the distribution of longitudinal and transverse residual stress on the central section of the substrate along line L2, which was 2 mm away from the upper surface of the substrate. The longitudinal residual stress was high tensile stress in the middle of the substrate and was compressive stress on both sides of the substrate. In Case B, Case C, and Case D, the longitudinal tensile stress peaks were located below the weld toes. With the increase in substrate thickness, the longitudinal tensile stress peaks (391 MPa, 383 MPa, 337 MPa) decreased gradually. The transverse tensile stress peaks appeared below the weld toes. In the area between the two weld toes, the transverse tensile stress decreased rapidly and turned into compressive stress. With the increase in substrate thickness, the peak value of the transverse tensile stress changed little, but the area of the high tensile stress gradually decreased. Case A and Case C were compared to illustrate the effect of the interpass temperature on the stress distribution. It could be seen that low interpass temperatures reduced the high tensile stress region and lowered the tensile stress peak but increased the transverse compressive stress peak in the middle of the substrate. Therefore, if only reductions in tensile residual stress are considered, a low interpass temperature is recommended for additive manufacturing. tensile stress gradually decreased. Case A and Case C were compared to illustrate the effect of the interpass temperature on the stress distribution. It could be seen that low interpass temperatures reduced the high tensile stress region and lowered the tensile stress peak but increased the transverse compressive stress peak in the middle of the substrate. Therefore, if only reductions in tensile residual stress are considered, a low interpass temperature is recommended for additive manufacturing.  Figure 12 shows the distribution of residual stress on L3. There was a large stress gradient near the Y309L/Q345 interface, which was mainly due to the thermal stress generated by the difference in the linear expansion coefficients of the two materials. In terms of the material parameters, the linear expansion coefficient of Y309L is about 40% larger than that of Q345. Inside the deposition layers, the longitudinal and transverse residual stresses at the bottom were significantly higher than those at the top. The thickness of the substrate determined the structural constraint of the workpiece-thus influencing the residual stress distributions. As the thickness of the substrate increased, the structural constraint of the workpiece increased correspondingly. As a result, both the high residual stress region and the residual stress peaks inside the deposition layers increased. If only reductions in the tensile residual stress in the deposition layers are considered, a thin substrate is recommended.   Figure 12 shows the distribution of residual stress on L3. There was a large stress gradient near the Y309L/Q345 interface, which was mainly due to the thermal stress generated by the difference in the linear expansion coefficients of the two materials. In terms of the material parameters, the linear expansion coefficient of Y309L is about 40% larger than that of Q345. Inside the deposition layers, the longitudinal and transverse residual stresses at the bottom were significantly higher than those at the top. The thickness of the substrate determined the structural constraint of the workpiece-thus influencing the residual stress distributions. As the thickness of the substrate increased, the structural constraint of the workpiece increased correspondingly. As a result, both the high residual stress region and the residual stress peaks inside the deposition layers increased. If only reductions in the tensile residual stress in the deposition layers are considered, a thin substrate is recommended. stress peak but increased the transverse compressive stress peak in the middle of the substrate. Therefore, if only reductions in tensile residual stress are considered, a low interpass temperature is recommended for additive manufacturing.  Figure 12 shows the distribution of residual stress on L3. There was a large stress gradient near the Y309L/Q345 interface, which was mainly due to the thermal stress generated by the difference in the linear expansion coefficients of the two materials. In terms of the material parameters, the linear expansion coefficient of Y309L is about 40% larger than that of Q345. Inside the deposition layers, the longitudinal and transverse residual stresses at the bottom were significantly higher than those at the top. The thickness of the substrate determined the structural constraint of the workpiece-thus influencing the residual stress distributions. As the thickness of the substrate increased, the structural constraint of the workpiece increased correspondingly. As a result, both the high residual stress region and the residual stress peaks inside the deposition layers increased. If only reductions in the tensile residual stress in the deposition layers are considered, a thin substrate is recommended.   Figure 13 shows the angular deformation evolution of the substrates in four cases. The thickness of the substrate influenced the variation trend and final value of the angular deformation. Comparing Case B (5 mm) and Case C (10 mm), although their final angular deformations were close, the evolution processes of their angular deformations were different. In Case B, the angular deformation increment was almost invariable during the first three layers, but increased remarkably in the 4th layer. In Case C, the angular deformation increment was large in the 1st layer, then decreased gradually in the subsequent three layers. Case D (20 mm) had the smallest angular deformation. Only slight angular deformation of the substrate occurred when the first layer was deposited. In the subsequent deposition process, the substrate was free from further angular deformation. It was worth noting that although Case A and Case C had different interpass temperatures, their evolution processes for the angular deformation were almost the same.

Deformation Evolution
ing to the large angular deformation increment in this layer. In Case C, the substrate was thicker than that in Case B, which led to their different angular deformation evolutions of the substrate. When depositing the 1st layer, the angular deformation increment was large due to the large temperature gradient in the thickness direction of the substrate. As the additive manufacturing process proceeded, the bending stiffness of the workpiece gradually increased. The resistance of the angular deformation increased gradually, leading to a smaller increment in angular deformation in the subsequent deposition process. In Case D, since the substrate was thick (20 mm), its high bending stiffness limited the angular deformation of the substrate and only a small degree of angular deformation occurred after the additive manufacturing. Therefore, if only the control of the angular deformation of the substrate is considered, a thick substrate is recommended. Figure 13. Angular deformation revolution of the substrate in four cases.
In the additive manufacturing process, the angular deformation of the substrate was due to the uneven transverse shrinkage in its thickness direction. The driving force was the temperature gradient in the thickness direction of the substrate, and the resistance was the bending stiffness of the substrate. In Case B, the substrate was thin (5 mm). When depositing the first layer, the driving force of the angular deformation was small due to the small temperature gradient in the thickness direction of the substrate. With the increase in deposition height, the temperature gradient increased-thus increasing the driving force of the angular deformation correspondingly. However, the bending stiffness of the substrate also increased. Therefore, the angular deformation increments of the 2nd and 3rd layers were almost unchanged. Figure 3 shows that compared with previous layers, the 4th layer has a small contact area with the 3rd layer. During the deposition of the 4th layer, the arc heat could not be conducted into the previous layers rapidly and accumulated in the 4th layer. Thus, the temperature gradient in the workpiece increased, leading to the large angular deformation increment in this layer. In Case C, the substrate was thicker than that in Case B, which led to their different angular deformation evolutions of the substrate. When depositing the 1st layer, the angular deformation increment was large due to the large temperature gradient in the thickness direction of the substrate. As the additive manufacturing process proceeded, the bending stiffness of the workpiece gradually increased. The resistance of the angular deformation increased gradually, leading to a smaller increment in angular deformation in the subsequent deposition process. In Case D, since the substrate was thick (20 mm), its high bending stiffness limited the angular deformation of the substrate and only a small degree of angular deformation occurred after the additive manufacturing. Therefore, if only the control of the angular deformation of the substrate is considered, a thick substrate is recommended.

1.
During the additive manufacturing process, the deposition materials at different positions experienced different thermal cycles, which might have led to the nonuniform microstructure and mechanical properties within the workpiece. Increasing the thickness of the substrate could effectively slow down the increase in the interpass temperature.

2.
The interpass temperature and the thickness of the substrate influenced the residual stress distribution in the additive manufactured structure. A low interpass temperature and thin substrate could effectively reduce the tensile residual stress. The weld toes suffered from tensile residual stresses in three directions. A thick substrate increased the tensile residual stresses and the risk of brittle fractures in the weld toes. 3.
The calculated results for the angular deformation of the substrate agreed well with the experimental results, verifying the reliability of the finite element method developed. Increasing the thickness of the substrate could effectively reduce the deformation of the substrate during the additive manufacturing process.