Weld Formation, Microstructure Evolution and Mechanical Property of Laser-Arc Hybrid Welded AZ31B Magnesium Alloy

: Laser-arc hybrid welding of AZ31B magnesium alloy was carried out in this paper, and the effects of welding parameters (laser power, welding speed, welding current) on weld formation, microstructure evolution and mechanical property were studied. The results showed that laser-arc hybrid welding can inhibit the undercut defect during laser welding on the one hand, and enhance the arc stability on the other hand. The penetration depth and width showed no signiﬁcant relation with the total heat input, but were linear related to the laser heat input and the arc heat input, respectively. The average grain size of the equiaxed grains was closely related to the heat input. The higher the heat input was, the larger the grains. The optimized welding parameters were laser power of 3.5 kW, welding speed of 1.8 m/min and welding current of 100 A. In this case, the weld was free of undercut and pores, and the tensile strength and elongation rate reached 190 MPa and 12%, respectively. distance between the wire and the laser on the sheet surface was 2 mm. Ar was employed as a protecting gas with ﬂow rate of 25 L/min. During welding, a high-speed camera was used to observe the plasma, with an acquisition rate of 4000 frames.


Introduction
Due to low density, high specific strength, stiffness and shock absorption, magnesium (Mg) alloy is one of the most favored materials to achieve energy conservation and emission reduction [1][2][3]. However, the weldability of Mg alloys is poor because of low boiling point, high vapor pressure and strong chemical activity.
Generally, Mg alloys are joined by friction stir welding, arc welding and laser welding. During friction stir welding, the processing temperature is low and the Mg is in the solid state; this is beneficial to improve the weldability of Mg alloys by reducing the forming tendency of pores and inclusions [4][5][6][7][8], which is also a problem in fusion joining of Alalloys [9,10]. However, the application in Mg alloys is limited, due to low efficiency and strict clamping accuracy. Metal insert gas (MIG) welding is one of the most used arc welding methods for industrial manufacturing, which can reduce the welding defects by filling of the wires. However, spatter formation is hard to avoid because of the low boiling point and high vapor pressure of the Mg alloy, plus the arc stability is poor and the weld grains are coarse due to large heat input [11,12]. Though arc stability can be improved by employing the variable polarity method [13], low efficiency is still the obstacle for application.
Laser welding has advantages of high energy density and low heat input, which is promising to obtain an excellent weld of Mg alloys with a high aspect ratio and narrow heataffected zone, as one of the most concerned methods for the welding of Mg alloys [14][15][16]. The heat-affected zone of the laser-welded Mg alloys can almost be ignored, and the grains are fine within the fusion zone, which is mainly composed of α-Mg and eutectic structure of Mg 17 Al 12 [17,18]. However, the welding stability and weld formation are poor because of element loss of Mg and Zn when the Mg alloys are irradiated by the high-energy laser, which also limits the application of laser welding in Mg alloys. 2 of 11 By combining the laser source and arc source, laser-arc hybrid welding can obtain a higher efficiency. Arc stability and the arc root drift can be improved by the attraction of the laser and arc [19][20][21], and a lower energy is needed for penetration. Moreover, the weld formation and quality can also be improved by the filling of wires, although relatively studies have been done [22,23] and systematic analyze on weld formation, microstructure and mechanical properties is lacking. Thus, laser-arc hybrid welding of AZ31B Mg alloy was carried out in this paper, the processing characteristics and weld formation were analyzed, and the microstructure and mechanical properties were discussed, which is beneficial to deepen the understanding of laser-arc hybrid welding of Mg alloys.

Materials and Methods
The base metal was an AZ31B magnesium (Mg) alloy with thickness of 12 mm and 7 mm, length of 200 mm and width of 100 mm. The filler metal was AZ31B magnesium wire with diameter of 1.2 mm, with chemical compositions shown in Table 1. Before welding, the sheet surface was steel brushed to remove the oxidation layer and cleaned by ethanol. The sheets with thickness of 12 mm were clamped for bead on plate welding, while those with thickness of 7 mm were clamped for butt welding. The laser-arc hybrid welding system consists of a laser source, a robot and an arc source, as shown in Figure 1. Parameters of arc welding and laser welding for comparison were listed in Table 2, and the detailed parameters for laser-arc hybrid welding were listed in Table 3. During laser-arc hybrid welding, a laser-leading mode with the laser at the front and the arc at the behind was employed. The angle between the arc torch and the horizontal plane was 55 • , the wire extension was 12 mm, and the distance between the wire and the laser on the sheet surface was 2 mm. Ar was employed as a protecting gas with flow rate of 25 L/min. During welding, a high-speed camera was used to observe the plasma, with an acquisition rate of 4000 frames. energy laser, which also limits the application of laser welding in Mg alloys.
By combining the laser source and arc source, laser-arc hybrid welding can o higher efficiency. Arc stability and the arc root drift can be improved by the attra the laser and arc [19][20][21], and a lower energy is needed for penetration. Moreov weld formation and quality can also be improved by the filling of wires, althoug tively studies have been done [22,23] and systematic analyze on weld formation, structure and mechanical properties is lacking. Thus, laser-arc hybrid welding of Mg alloy was carried out in this paper, the processing characteristics and weld for were analyzed, and the microstructure and mechanical properties were discussed is beneficial to deepen the understanding of laser-arc hybrid welding of Mg alloys

Materials and Methods
The base metal was an AZ31B magnesium (Mg) alloy with thickness of 12 mm mm, length of 200 mm and width of 100 mm. The filler metal was AZ31B magnesiu with diameter of 1.2 mm, with chemical compositions shown in Table 1. Before w the sheet surface was steel brushed to remove the oxidation layer and cleaned by e The sheets with thickness of 12 mm were clamped for bead on plate welding, whi with thickness of 7 mm were clamped for butt welding. The laser-arc hybrid welding system consists of a laser source, a robot and source, as shown in Figure 1. Parameters of arc welding and laser welding for com were listed in Table 2, and the detailed parameters for laser-arc hybrid welding wer in Table 3. During laser-arc hybrid welding, a laser-leading mode with the lase front and the arc at the behind was employed. The angle between the arc torch horizontal plane was 55°, the wire extension was 12 mm, and the distance betw wire and the laser on the sheet surface was 2 mm. Ar was employed as a protect with flow rate of 25 L/min. During welding, a high-speed camera was used to obse plasma, with an acquisition rate of 4000 frames.     After welding, the surface appearance was recorded by camera, and the metallographic samples and tensile samples were prepared. The metallographic samples were, firstly, chemically polished with a solution containing glycerinum of 20 mL, hydrochloric acid of 2 mL, nitric acid of 3 mL and acetic acid of 5 mL. Then, the samples were chemically etched with solution containing 1 g of oxalic acid, 1 mL of acetic acid, 1 mL of nitric acid and 150 mL of deionized water. The cross-sectional morphologies were observed by optical microscope finally. The grain size of the equiaxed grains within the weld microstructures was obtained using Image J software, which was calculated as equivalent diameter, and the result was the average value from 5 images. The schematic diagram of the tensile samples was shown in Figure 2. The tensile test was carried out with loading rate of 0.5 mm/min, and the fracture surfaces were observed by a scanning electron microscope. After welding, the surface appearance was recorded by camera, and graphic samples and tensile samples were prepared. The metallographic s firstly, chemically polished with a solution containing glycerinum of 20 mL, acid of 2 mL, nitric acid of 3 mL and acetic acid of 5 mL. Then, the samples we etched with solution containing 1 g of oxalic acid, 1 mL of acetic acid, 1 mL and 150 mL of deionized water. The cross-sectional morphologies were obse cal microscope finally. The grain size of the equiaxed grains within the wel tures was obtained using Image J software, which was calculated as equival and the result was the average value from 5 images. The schematic diagram samples was shown in Figure 2. The tensile test was carried out with loadi mm/min, and the fracture surfaces were observed by a scanning electron mi

Comparison of Welding Processes
As shown in Figure 3, welding plasma was observed during arc weldi arc hybrid welding. It was found that the arc column was distributed along during arc welding. Due to the high vapor pressure of the magnesium allo umn fluctuated due to unstable burning of the filler wire. During laser-arc ing, a keyhole was induced within the base material by the laser beam with density, and the plasma with abundant ions and electrons was then formed surface, due to the eruption of the metallic vapor forming the keyhole. The could provide cathode spots and attract the arc column, which promoted the electric channel between the laser plasma and the arc column. In this case, th was easily attracted by the introduced laser, compressed by the electric chan concentrated, which enhanced the arc stability.

Comparison of Welding Processes
As shown in Figure 3, welding plasma was observed during arc welding and laser-arc hybrid welding. It was found that the arc column was distributed along the wire axis during arc welding. Due to the high vapor pressure of the magnesium alloy, the arc column fluctuated due to unstable burning of the filler wire. During laser-arc hybrid welding, a keyhole was induced within the base material by the laser beam with high energy density, and the plasma with abundant ions and electrons was then formed on the sheet surface, due to the eruption of the metallic vapor forming the keyhole. The laser plasma could provide cathode spots and attract the arc column, which promoted the formation of electric channel between the laser plasma and the arc column. In this case, the arc column was easily attracted by the introduced laser, compressed by the electric channel and more concentrated, which enhanced the arc stability.
The surface and cross-sectional morphologies of the arc weld, laser weld and laser-arc hybrid weld of AZ31B Mg alloy were shown in Figure 4. For the arc weld, the weld surface was discontinuous, and there was nearly no penetration depth with the filler wires accumulated on the sheet surface. The penetration depth of the laser weld was large, but defects of undercut and pores occurred easily. Relatively, the laser-arc hybrid weld was composed of a wide upper arc zone and a narrow lower laser zone, with continuous and full filling on the surface as well as eliminated pores within the cross-section.
Due to the low density of the Mg alloys, the gravity promoting the droplet transfer was small, and a larger electromagnetic force was needed to achieve droplet transfer during MIG arc welding; the current density of the anode spot on the drop surface was then enlarged, which accelerated the evaporation of the drops, and the droplet transfer was hindered. Moreover, the vapor pressure increased rapidly due to the low boiling point of the Mg alloy, so an explosion of the drops then easily occurred even with slight overheating, which promoted the spatter formation and arc interruption [24]. Thus, the welding stability of the arc welding was poor, and a continuous weld was difficult to form. During laser welding, the elements of Mg and Zn with a low boiling point were easily evaporated by the high-energy laser beam, which induced an obvious undercut defect. Relatively, the electrical resistivity of the laser plasma was low during laser-arc hybrid welding, as a larger current density can be loaded for the hybrid plasma with a higher energy density and penetration ability for the arc. It should be noted that pore inhibition was also obtained for laser-arc hybrid welding, due to a larger volume and slower cooling rate compared with laser welding, ensuring enough time for the pores to escape from the molten pool.

Comparison of Welding Processes
As shown in Figure 3, welding plasma was observed during arc welding an arc hybrid welding. It was found that the arc column was distributed along the w during arc welding. Due to the high vapor pressure of the magnesium alloy, the umn fluctuated due to unstable burning of the filler wire. During laser-arc hybri ing, a keyhole was induced within the base material by the laser beam with high density, and the plasma with abundant ions and electrons was then formed on th surface, due to the eruption of the metallic vapor forming the keyhole. The laser could provide cathode spots and attract the arc column, which promoted the form electric channel between the laser plasma and the arc column. In this case, the arc was easily attracted by the introduced laser, compressed by the electric channel an concentrated, which enhanced the arc stability.   The surface and cross-sectional morphologies of the arc weld, laser weld and laserarc hybrid weld of AZ31B Mg alloy were shown in Figure 4. For the arc weld, the weld surface was discontinuous, and there was nearly no penetration depth with the filler wires accumulated on the sheet surface. The penetration depth of the laser weld was large, but defects of undercut and pores occurred easily. Relatively, the laser-arc hybrid weld was composed of a wide upper arc zone and a narrow lower laser zone, with continuous and full filling on the surface as well as eliminated pores within the cross-section. Due to the low density of the Mg alloys, the gravity promoting the droplet transfer was small, and a larger electromagnetic force was needed to achieve droplet transfer during MIG arc welding; the current density of the anode spot on the drop surface was then enlarged, which accelerated the evaporation of the drops, and the droplet transfer was hindered. Moreover, the vapor pressure increased rapidly due to the low boiling point of the Mg alloy, so an explosion of the drops then easily occurred even with slight overheating, which promoted the spatter formation and arc interruption [24]. Thus, the welding stability of the arc welding was poor, and a continuous weld was difficult to form. During laser welding, the elements of Mg and Zn with a low boiling point were easily evaporated by the high-energy laser beam, which induced an obvious undercut defect. Relatively, the electrical resistivity of the laser plasma was low during laser-arc hybrid welding, as a larger current density can be loaded for the hybrid plasma with a higher energy density and penetration ability for the arc. It should be noted that pore inhibition was also obtained for laser-arc hybrid welding, due to a larger volume and slower cooling rate compared with laser welding, ensuring enough time for the pores to escape from the molten pool.  As shown in Figure 5, under the given welding speed of 1.8 m/min and welding current of 100 A, all the welds were continuous and uniform, while the density of the perlage at the weld surface decreased with the laser power increasing from 3 kW to 5 kW. Specifically, local collapse occurred with the laser power ranging between 4.5 kW and 5 kW because of excessive energy. In this case, the laser energy entering the inner sheet was unstable, due to strong metallic vapor, which causes spatter formation and decreased welding stability. Under the given laser power of 4 kW and welding current of 100 A, it was fou whether the welding speed excessive high or low, the weld formation was poor. hand, the heat input was excessive with low welding speed, so it was difficult molten metal was to be held up by the surface tension, which induced local colla the other hand, the arc stability decreased at a high welding speed, which deterior weld formation.
Under the given laser power of 4 kW and welding speed of 1.8 m/min, th were widened with an increase in the welding current. Moreover, some spatters w ible because of poor arc stability with a welding current of 50 A, while overhea duced explosion of the molten drops occurred with a welding current of 150 A excessive arc power.
As shown in Figures 6 and 7, the cross-sectional morphologies were acceptab out the undercut defect. Under the given welding speed of 1.8 m/min and welding of 100 A, the penetration depth and width were similar at 6.5 mm with laser pow kW, and increased to 10.7 mm and 7.9 mm with the laser power increased to 5 kW tively. For each increase of l kW of laser power, the penetration depth and width in 2.1 mm and 0.65 mm, respectively, with a more significant effect on penetration Though the penetration depth achieved the largest at a laser power of 5 kW, the up Under the given laser power of 4 kW and welding current of 100 A, it was found that whether the welding speed excessive high or low, the weld formation was poor. On one hand, the heat input was excessive with low welding speed, so it was difficult for the molten metal was to be held up by the surface tension, which induced local collapse. On the other hand, the arc stability decreased at a high welding speed, which deteriorated the weld formation.
Under the given laser power of 4 kW and welding speed of 1.8 m/min, the welds were widened with an increase in the welding current. Moreover, some spatters were visible because of poor arc stability with a welding current of 50 A, while overheating induced explosion of the molten drops occurred with a welding current of 150 A, due to excessive arc power.
As shown in Figures 6 and 7, the cross-sectional morphologies were acceptable without the undercut defect. Under the given welding speed of 1.8 m/min and welding current of 100 A, the penetration depth and width were similar at 6.5 mm with laser power of 3 kW, and increased to 10.7 mm and 7.9 mm with the laser power increased to 5 kW, respectively. For each increase of l kW of laser power, the penetration depth and width increased 2.1 mm and 0.65 mm, respectively, with a more significant effect on penetration depth. Though the penetration depth achieved the largest at a laser power of 5 kW, the upper surface was underfilled, which may be related to element loss with excessive laser energy.     Under the given laser power of 4 kW and welding current of 100 A, the penetration depth and width were similar at 10.3 mm with welding speed of 1.2 m/min, and decreased to 7.9 mm and 6.4 mm with the welding speed increased to 2.4 m/min, respectively. With an increase in welding speed, the energy entering the inner sheet decreased, with a weakened penetration depth, while the penetration width decreased because of a reduced function area of the arc on the sheet surface. For each increase of 0.3 m/min in welding speed, the penetration depth and width decreased 0.65 mm and 0.9 mm, respectively, with a more significant effect on penetration width.
Under the given laser power of 4 kW and welding speed of 1.8 m/min, the penetration depth almost kept at about 9 mm, while the penetration width increased from 5.6 mm to 9.6 mm when the welding current increased from 50 A to 150 A. For each increase of 25 A of welding current, the penetration width increased about 1 mm, due to a larger function area of the arc on the sheet surface. Generally, the coupling of the laser and arc was enhanced by increasing the welding current, which was beneficial for penetration depth. However, the arc stability was weakened due to overheating of the molten drops at excessive welding current, and the laser-arc interaction was actually decreased because of a smaller difference in electron density between the laser plasma and arc column. Thus, the penetration depth was insusceptible to the welding current.

Relationship between Heat Input and Weld Formation
Generally, the penetration depth and width were closely related to the heat input (H, calculated by Equation (1), [25]), which was not suited for laser-arc hybrid welding of Mg alloy in this study, as shown in Figure 8a. Considering that penetration ability was mainly dependent on the keyhole formed by the laser, and the penetration width was closely related to the spreading of the filler wire by the arc, laser heat input (H L ) and arc heat input (H A ) were proposed, which can be calculated by Equations (2) and (3), respectively. Then, new relations were established, as shown in Figure 8b,c. It can be found that the penetration depth and width were linear related to H L and H A , respectively. For each increase of 500 J/cm of the H L and H A , the depth and width increased about 1.8 mm and 2.7 mm, respectively. H = (P + U·I)/v (1) where, the H, H L and H A were total heat input, laser heat input and arc heat input, respectively. P was laser power, U was welding voltage, I was welding current and v was welding speed.
Metals 2022, 12, x FOR PEER REVIEW 7 of 11 the penetration depth and width decreased 0.65 mm and 0.9 mm, respectively, with a more significant effect on penetration width. Under the given laser power of 4 kW and welding speed of 1.8 m/min, the penetration depth almost kept at about 9 mm, while the penetration width increased from 5.6 mm to 9.6 mm when the welding current increased from 50 A to 150 A. For each increase of 25 A of welding current, the penetration width increased about 1 mm, due to a larger function area of the arc on the sheet surface. Generally, the coupling of the laser and arc was enhanced by increasing the welding current, which was beneficial for penetration depth. However, the arc stability was weakened due to overheating of the molten drops at excessive welding current, and the laser-arc interaction was actually decreased because of a smaller difference in electron density between the laser plasma and arc column. Thus, the penetration depth was insusceptible to the welding current.

Relationship between Heat Input and Weld Formation
Generally, the penetration depth and width were closely related to the heat input (H, calculated by Equation (1), [25]), which was not suited for laser-arc hybrid welding of Mg alloy in this study, as shown in Figure 8a. Considering that penetration ability was mainly dependent on the keyhole formed by the laser, and the penetration width was closely related to the spreading of the filler wire by the arc, laser heat input (HL) and arc heat input (HA) were proposed, which can be calculated by Equations (2) and (3), respectively. Then, new relations were established, as shown in Figure 8b,c. It can be found that the penetration depth and width were linear related to HL and HA, respectively. For each increase of 500 J/cm of the HL and HA, the depth and width increased about 1.8 mm and 2.7 mm, respectively.
where, the H, HL and HA were total heat input, laser heat input and arc heat input, respectively. P was laser power, U was welding voltage, I was welding current and v was welding speed.

Microstructure Evolutions
Considering the interaction of the laser source and arc source as well as the filler wire matched with the base metal in this study, the microstructure evolution within the upper arc zone were more significant compared with the laser zone. Thus, the microstructure characteristics at the center of the wide upper arc zone on the cross-sectional samples were compared. As shown in Figure 9, equiaxed grains with a snowflake shape existed within the center of the arc zone for all the welds, since the dendritic structure tended to grow up along the close-packed direction according to the hexagonal structure of the Mg alloy.
the center of the arc zone for all the welds, since the dendritic structure te up along the close-packed direction according to the hexagonal structure of With laser power increased from 3 kW to 5 kW, the average size of grains increased from 25 μm to 50 μm, with the quantity reduced. The aver also reached about 48 μm at a welding speed of 1.2 m/min, which was kept the welding speed ranging between 1.5 m/min and 2.1 m/min, and, finally about 28 μm with the welding speed further increased to 2.4 m/min. Relativ ing current showed a smaller effect on grain size, as the grain size increase to 36 μm when the welding current increased from 50 A to 150 A. Overall, of the equiaxed grains was closely related to the heat input. The larger the h the lower the cooling rate of the molten pool, which induced adequate time f of the grains.

Weld Tensile Properties
As shown in Figure 10, under the given welding speed of 1.8 m/min current of 100 A, tensile strength decreased from 185 MPa to 150 MPa with th increased from 3 kW to 5 kW, while the elongation rate remained at 12% w power was between 3 kW and 4 kW, decreasing to 5% when the laser powe 5 kW. Under the given laser power of 4 kW and welding current of 100 A, te and elongation rate remained at 180 MPa and 12% with the welding spe m/min, and dramatically decreased to 145 MPa and 4%, respectively, whe speed reached 2.4 m/min. Under the given laser power of 4 kW and weldin m/min, the elongation rate decreased from 12% to 6.5% when the weldin creased from 50 A to 150 A, while the tensile strength remained at 170 M With laser power increased from 3 kW to 5 kW, the average size of the equiaxed grains increased from 25 µm to 50 µm, with the quantity reduced. The average grain size also reached about 48 µm at a welding speed of 1.2 m/min, which was kept at 35 µm with the welding speed ranging between 1.5 m/min and 2.1 m/min, and, finally, decreased to about 28 µm with the welding speed further increased to 2.4 m/min. Relatively, the welding current showed a smaller effect on grain size, as the grain size increased from 30 µm to 36 µm when the welding current increased from 50 A to 150 A. Overall, the grain size of the equiaxed grains was closely related to the heat input. The larger the heat input was, the lower the cooling rate of the molten pool, which induced adequate time for the growth of the grains.

Weld Tensile Properties
As shown in Figure 10, under the given welding speed of 1.8 m/min and welding current of 100 A, tensile strength decreased from 185 MPa to 150 MPa with the laser power increased from 3 kW to 5 kW, while the elongation rate remained at 12% when the laser power was between 3 kW and 4 kW, decreasing to 5% when the laser power increased to 5 kW. Under the given laser power of 4 kW and welding current of 100 A, tensile strength and elongation rate remained at 180 MPa and 12% with the welding speed below 2.1 m/min, and dramatically decreased to 145 MPa and 4%, respectively, when the welding speed reached 2.4 m/min. Under the given laser power of 4 kW and welding speed of 1.8 m/min, the elongation rate decreased from 12% to 6.5% when the welding current increased from 50 A to 150 A, while the tensile strength remained at 170 MPa when the welding current was below 125 A, decreasing to 150 MPa when the welding current increased to 150 A. Overall, the tensile strength and elongation rate decreased with an increase in laser energy or arc energy, which also deteriorated at a high welding speed because of a lack of filling. etals 2022, 12, x FOR PEER REVIEW welding current was below 125 A, decreasing to 150 MPa when the weldi creased to 150 A. Overall, the tensile strength and elongation rate decreas crease in laser energy or arc energy, which also deteriorated at a high weld cause of a lack of filling.  As shown in Figure 11, all the fracture surfaces were characterized as cleavage mode, whether fractured along the base metal (Figure 11a,f), weld metal (Figure 11b) or heataffected zone (Figure 11c-e) during tensile tests. Differently, the fracture surface along the base metal was flat with a river pattern, while the fracture surfaces along the weld metal and heat-affected zone were presented as a fluctuated cleavage unit with visible cracks, due to an excessive heat input with laser power of 5 kW, or insufficient filling at the welding speed of 2.4 m/min or welding current of 50 A. affected zone (Figure 11c-e) during tensile tests. Differently, the fracture sur base metal was flat with a river pattern, while the fracture surfaces along t and heat-affected zone were presented as a fluctuated cleavage unit with due to an excessive heat input with laser power of 5 kW, or insufficient fillin ing speed of 2.4 m/min or welding current of 50 A.

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A large penetration depth and sound weld formation of Mg alloys can be obtained by laser-arc hybrid welding. The undercut defect can be inhibited by the filling of wires, while the pores can be eliminated by the large volume and slow cooling rate of the molten pool.

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The penetration depth and width were not significantly related to the total heat input, but showed a linear relation with the laser heat input and arc heat input, respectively.

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The grain size of the equiaxed grains was closely related to the heat input. The higher the heat input was, the lower the cooling rate of the molten pool, which induced adequate time for growth of the grains.

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The tensile strength and elongation rate decreased with an increase in laser energy or arc energy, which also deteriorated at a high welding speed because of a lack of filling. Many cracks occurred at the fracture surface with excessive power or insufficient filling. The optimized welding parameters were a laser power of 3.5 kW, welding speed of 1.8 m/min and welding current of 100 A. In this case, the tensile strength and elongation rate reached 190 MPa and 12%, respectively.
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Data Availability Statement: Not applicable.