Effects of Al-Si Coating on Static and Dynamic Strength of Spot-Welded Hot-Stamping Steel Joints

: Al-Si is the most popular coating used to prevent oxidation on the surfaces of hot-stamped steel sheets during the heating process. However, like other coatings, it affects the strength of the spot welds in joining the hot-stamped steel parts. In this study, the effects of Al-Si coating on the tensile strength of the resistance spot-welded joints in hot-stamped steel are discussed. Two types of 1.8 mm hot-stamped steel, in uncoated and Al-Si coated forms, were resistance spot-welded, and the tensile shear behavior of the welded joints was studied in both static and dynamic tests. To do this, a special ﬁxture for impact tensile shear tests was designed and fabricated. In the case of the Al-Si coated steel, the presence of the molten Al-Si over the fusion zone, especially its aggregation in the edge of the weld nugget, caused a decrease in the maximum tensile load capacity and a failure of energy absorption in static and dynamic tests, respectively. Additionally, it increased the probability of changing its failure mode from pull out to interfacial fracture in the dynamic test. This study shows that the tensile strength behavior of the welded joints for the Al-Si coated hot-stamped steel is lower than the uncoated steel during static, and especially dynamic, force.


Introduction
As a major point of concern in recent years, the automotive industry has been seeking to increase the strength of vehicle bodies to improve their crashworthiness while also decreasing their overall weight in order to reduce fuel consumption and air pollution. To this end, ultra-high-strength steels (UHSS) have been employed [1][2][3]. Furthermore, the monocoque structure of car bodies makes the integrity of the joints between the parts as influential as the strength of each individual part on the overall strength of the structure. Therefore, the quality of the welded joints of these parts, usually using resistance spot welding (RSW), is highly important. RSW is based on Joule's heating, which depends on the electrical resistance of the sheets stack. Contact resistance shares a substantial portion of the electrical resistance and is very sensitive to both surface roughness and coating type [4]. Press hardenable steels (PHS) are considered to be one of the most applicable UHSS formed through the hot-stamping process. As these parts should be heated up to 910 • C for austenitization purpose, severe oxidation occurs on the surface of these parts upon exposure to air [5]. Various coatings such as Al-Si and Zn have thus far been taken into consideration for preventing oxidation during the heating process [6]. However, while coating will protect steel sheets against surface oxidation, it will also affect their weldability. Cha et al. reported that welding parameters for Al-coated steel, compared to those for uncoated steel, are different because of the differences in the Al-coated layer and base metal properties such as electrical resistivity and melting point [7]. Over the last decade, some studies have been conducted on investigating the effects of coating on resistance spot-welding of hot-stamped steels. Cheon et al. reported that in the case of RSW of Zn coated PHS, spatter occurred at low current because of quick heat generation in the faying interface. They proposed an optimized pulse current to improve the appropriate welding current range [8]. Ji et al. investigated the effects of Al-Si and Zn coating on the nugget geometry of hot-stamped boron steel and showed that in the presence of Al-Si coating, the acceptable welding current was wide enough (while there was no weldable current fund for Zn coating) [9]. Ighodaro et al. compared the effects of galvannealed and Al-Si coatings on the weldability of hot-stamped steels. They expressed that the coating influences the appropriate welding current because of the different electrical resistances that arise from different coatings [10].
To ensure the safety of passengers and meet safety standards and regulations, vehicle design engineers require an adequate knowledge of welded joint failure behavior in addition to the mechanical properties of their materials. Various standards and tests have been proposed and applied to study the failure mechanisms and measure the strength of resistance spot-welded joints. Static tests such as cross tension, tensile shear, and peel tests are employed to evaluate welded joints during static loading, whereas dynamic tests (such as the impact test) are used to determine the dynamic properties of them [11]. Interfacial failure (IF) and pullout failure (PO) are recognized as the two main failure modes of welded joints [12]. Choi et al. studied the RSW between GA780DP steel and PHS by performing tensile shear tests in order to determine the effects of welding currents on welded joint strength. They reported that by increasing the weld current, the nugget diameter increases and improves welded joint strength [13]. Zhang et al. analyzed the failure phenomenon of RSW joints in DP steels during the tensile shear test and reported that by increasing welding current, the failure mode changes from IF to PO [14]. Ighodaro et al. found that the coating type (Al-Si/galvanneald) of hot-stamped steels does not have any influence on the peak failure load and the energy absorption of the joints, but that the types of coating affect the failure mode transition of welded joints. The failure mode transition from IF to PO for Al-Si coated samples occurs at smaller nugget sizes compared to galvanealed coated samples [10]. Zhang et al. compared resistance spot-welding of Al-Si coated and uncoated 22MnB5 boron steel to Mg. They reported that the presence of Al-Si coating improves the peak load, fracture elongation, and energy absorption of the welded joint during the tensile shear test [15]. Li et al. studied the influence of welding parameters on the tensile shear strength of hot-stamped annealed steel-welded joints. They asserted that the welding current has the greatest effect on the tensile shear strength of welded joints [16]. Liang et al. investigated the effect of welding current on the tensile shear strength of welded joints for the RSW of hot-stamped 22MnB5 and HSLA350 steel sheets and observed different types of failure modes during their tests [17]. Paveebunvipak et al. analyzed and compared the static performance and failure characteristics of the RSW of hot stamping steel grade 22MnB5 and as-rolled high-strength steel grade 1000 by carrying out a tensile shear test and cross-tension test on welded samples. They reported that the maximum load-carrying capacity and absorbed energy were observed in RSW samples of steel grade 1000 [18]. Tan et al. investigated the effect of Al-Si coating on the tensile shear fracture behavior of the RSW of press-hardened steel grade 22MnB5. They found that Fe-(Al,Si) on the edge of weld nuggets acted as a crack source and imitated the fracture [19]. However, these studies do not compare the tensile shear strength of welded joints between coated and uncoated steel in order to determine the effects of Al-Si coating on the tensile properties of hot-stamped steels. Chen et al. studied the effect of Al-Si coating on the mechanical performance of RSW of press-hardened steel by carrying out a lap shear test and cross-tension test on welded samples of both Al-Si coated and uncoated forms of steel. They found that in the presence of Al-Si coating, the mechanical performance of welded joints is lower than in uncoated forms. In this study, in order to provide uncoated steel, the Al-Si coating at the faying interface was removed by diamond grinding [20], which resulted in different surface properties than those found on rolled sheets. On the other hand, most previous studies have been based on static tests without performing dynamic tests. The complexity of dynamic tests, due to their reliance on various equipment, has led to their limited application [21]. The present study evaluates the effect of Al-Si coating on both the static and dynamic strength of spot-welds in one type of hot-stamping steel.

Material Specifications
The primary microstructure of the steel used in the hot-stamping process consists of ferrite and pearlite with a tensile strength of about 500 MPa. During hot-stamping, a blank is first heated in an approximate temperature of 910 • C in order to become austenitic. Next, the blank is formed and quenched simultaneously. It is cooled and quenched by cooling ducts existing in the die. This process creates a martensitic microstructure in the part and, as a result, improves its strength up to approximately 1500 MPa [6]. The material used in this study was Usibor1500 steel in both the uncoated and Al-Si coated forms. The thickness of both types of selected steels was 1.8 mm. The chemical compositions of these two sheets of steel are reported in Table 1. The steels underwent the hot-stamping process under similar conditions. They were austenitized for 6 min at 910 • C, and then they were quenched. The oxidation formed on the surface of the uncoated steel was removed through sandblasting.

Microstructure
Metallographic sections of the coated steels were catered before and after quenching in order to measure the thickness of the coating and to determine the microstructure of the material. Figure 1 illustrates the substructure and formed changes in the thickness of the Al-Si coating before and after the hot-stamping operation. The microstructure of the raw material is a combination of ferrite and pearlite, which was converted into a martensite microstructure after hot-stamping. On the other hand, after hot-stamping, the Al-Si coating diffused to the base metal, transformed into an alloyed intermetallic layer, and the average thickness of the layer increased from 27 µm to 37 µm. This coating layer structure consists of Al-Fe-Si and different intermetallic compounds of α-Fe with Al and Si in a solid solution (e.g., FeAl 2 and Fe 2 SiAl 2 ) [9,22,23].
Metals 2021, 11, x FOR PEER REVIEW 3 of 12 dynamic tests. The complexity of dynamic tests, due to their reliance on various equipment, has led to their limited application [21]. The present study evaluates the effect of Al-Si coating on both the static and dynamic strength of spot-welds in one type of hotstamping steel.

Material Specifications
The primary microstructure of the steel used in the hot-stamping process consists of ferrite and pearlite with a tensile strength of about 500 MPa. During hot-stamping, a blank is first heated in an approximate temperature of 910 °C in order to become austenitic. Next, the blank is formed and quenched simultaneously. It is cooled and quenched by cooling ducts existing in the die. This process creates a martensitic microstructure in the part and, as a result, improves its strength up to approximately 1500 MPa [6]. The material used in this study was Usibor1500 steel in both the uncoated and Al-Si coated forms. The thickness of both types of selected steels was 1.8 mm. The chemical compositions of these two sheets of steel are reported in Table 1. The steels underwent the hot-stamping process under similar conditions. They were austenitized for 6 min at 910 °C, and then they were quenched. The oxidation formed on the surface of the uncoated steel was removed through sandblasting.

Microstructure
Metallographic sections of the coated steels were catered before and after quenching in order to measure the thickness of the coating and to determine the microstructure of the material. Figure 1 illustrates the substructure and formed changes in the thickness of the Al-Si coating before and after the hot-stamping operation. The microstructure of the raw material is a combination of ferrite and pearlite, which was converted into a martensite microstructure after hot-stamping. On the other hand, after hot-stamping, the Al-Si coating diffused to the base metal, transformed into an alloyed intermetallic layer, and the average thickness of the layer increased from 27 μm to 37 μm. This coating layer structure consists of Al-Fe-Si and different intermetallic compounds of α-Fe with Al and Si in a solid solution (e.g., FeAl2 and Fe2SiAl2) [9,22,23].

Mechanical Tests
In order to determine the effects of Al-Si coating on the static strength of welded joints, the tensile shear test was performed. According to ISO 14273, the coated and uncoated steels were cut into 105 mm × 30 mm pieces for preparing static tensile shear specimens [24]. The dimensions and overlap are shown in Figure 2. The initial free span between the clamps was 95 mm.

Mechanical Tests
In order to determine the effects of Al-Si coating on the static strength of welded joints, the tensile shear test was performed. According to ISO 14273, the coated and uncoated steels were cut into 105 mm × 30 mm pieces for preparing static tensile shear specimens [24]. The dimensions and overlap are shown in Figure 2. The initial free span between the clamps was 95 mm. The cut pieces underwent a thermal process similar to the hot-stamping process. The oxides formed on uncoated pieces were removed using a sandblasting machine. Tensile shear tests were performed on a 100 kN servo-hydraulic test machine at a crosshead speed of 1 mm/min.
The dynamic impact test is a method for determining the dynamic properties of resistance spot-welding. Different kinds of impact tests such as tensile shear and cross tension can be conducted by using the required fixtures. The typical methods of impact tests on spot welding joints are realized using either a pendulum machine or a drop tower. A pendulum machine contains a fixed and movable part and is equipped by a U-shaped hammer developed by Bayraktar et al. according to the idea of Grumbach and Sanz [1].
The most common impact testing system is a drop tower. Chao et al. developed a drop weight machine for spot-welded joints. They added some details to an original drop weight machine to make it appropriate for testing welded joints [25]. In order to investigate the effects of Al-Si coating on the dynamic behavior of welded joints, some impact tensile shear tests on spot-welded joints by using a drop test machine were performed. Based on the ISO14323 standard procedure, the coated and uncoated steels were cut into 105 mm × 45 mm pieces [26]. The dimensions and overlap of the impact tensile shear test specimen are shown in Figure 3. The initial free span between the clamps was 95 mm. Similar to static test samples, the cut pieces underwent a thermal process similar to hot-stamping and the samples were sandblasted to remove the oxides formed on uncoated pieces. A Tecna 8105 AC (Tecna SA, Bologna, Italy) welding machine was used for The cut pieces underwent a thermal process similar to the hot-stamping process. The oxides formed on uncoated pieces were removed using a sandblasting machine. Tensile shear tests were performed on a 100 kN servo-hydraulic test machine at a crosshead speed of 1 mm/min.
The dynamic impact test is a method for determining the dynamic properties of resistance spot-welding. Different kinds of impact tests such as tensile shear and cross tension can be conducted by using the required fixtures. The typical methods of impact tests on spot welding joints are realized using either a pendulum machine or a drop tower. A pendulum machine contains a fixed and movable part and is equipped by a U-shaped hammer developed by Bayraktar et al. according to the idea of Grumbach and Sanz [1].
The most common impact testing system is a drop tower. Chao et al. developed a drop weight machine for spot-welded joints. They added some details to an original drop weight machine to make it appropriate for testing welded joints [25]. In order to investigate the effects of Al-Si coating on the dynamic behavior of welded joints, some impact tensile shear tests on spot-welded joints by using a drop test machine were performed. Based on the ISO14323 standard procedure, the coated and uncoated steels were cut into 105 mm × 45 mm pieces [26]. The dimensions and overlap of the impact tensile shear test specimen are shown in Figure 3. The initial free span between the clamps was 95 mm.

Mechanical Tests
In order to determine the effects of Al-Si coating on the static strength of welded joints, the tensile shear test was performed. According to ISO 14273, the coated and uncoated steels were cut into 105 mm × 30 mm pieces for preparing static tensile shear specimens [24]. The dimensions and overlap are shown in Figure 2. The initial free span between the clamps was 95 mm. The cut pieces underwent a thermal process similar to the hot-stamping process. The oxides formed on uncoated pieces were removed using a sandblasting machine. Tensile shear tests were performed on a 100 kN servo-hydraulic test machine at a crosshead speed of 1 mm/min.
The dynamic impact test is a method for determining the dynamic properties of resistance spot-welding. Different kinds of impact tests such as tensile shear and cross tension can be conducted by using the required fixtures. The typical methods of impact tests on spot welding joints are realized using either a pendulum machine or a drop tower. A pendulum machine contains a fixed and movable part and is equipped by a U-shaped hammer developed by Bayraktar et al. according to the idea of Grumbach and Sanz [1].
The most common impact testing system is a drop tower. Chao et al. developed a drop weight machine for spot-welded joints. They added some details to an original drop weight machine to make it appropriate for testing welded joints [25]. In order to investigate the effects of Al-Si coating on the dynamic behavior of welded joints, some impact tensile shear tests on spot-welded joints by using a drop test machine were performed. Based on the ISO14323 standard procedure, the coated and uncoated steels were cut into 105 mm × 45 mm pieces [26]. The dimensions and overlap of the impact tensile shear test specimen are shown in Figure 3. The initial free span between the clamps was 95 mm. Similar to static test samples, the cut pieces underwent a thermal process similar to hot-stamping and the samples were sandblasted to remove the oxides formed on uncoated pieces. A Tecna 8105 AC (Tecna SA, Bologna, Italy) welding machine was used for Similar to static test samples, the cut pieces underwent a thermal process similar to hot-stamping and the samples were sandblasted to remove the oxides formed on uncoated pieces. A Tecna 8105 AC (Tecna SA, Bologna, Italy) welding machine was used for performing resistance spot welds. The exact values of the current and force were measured using a Rogowski coil and piezoelectric load cell. According to AWS D8.9, the welding electrode was RWMA group A, Class 2, truncated cone nose, with a face diameter of 8 mm [27]. The welding parameters for preparing test specimens were selected based on some previous practical welding experiences using these types of material. The electrode Metals 2021, 11, 976 5 of 12 force was adjusted to 5.7 kN and all welds were performed in 3 pulses. Since the aim was to achieve the maximum possible tensile strength of the welded joints, the selected parameters were at the acceptable range of weldability and mainly close to the expulsion condition. Representative cross-sections for both coated and uncoated sheets are shown in Figure 4 with a welding current of 8.2 kA applied over 9 cycles in 3 pulses.
performing resistance spot welds. The exact values of the current and force were measured using a Rogowski coil and piezoelectric load cell. According to AWS D8.9, the welding electrode was RWMA group A, Class 2, truncated cone nose, with a face diameter of 8 mm [27]. The welding parameters for preparing test specimens were selected based on some previous practical welding experiences using these types of material. The electrode force was adjusted to 5.7 kN and all welds were performed in 3 pulses. Since the aim was to achieve the maximum possible tensile strength of the welded joints, the selected parameters were at the acceptable range of weldability and mainly close to the expulsion condition. Representative cross-sections for both coated and uncoated sheets are shown in Figure 4 with a welding current of 8.2 kA applied over 9 cycles in 3 pulses.  To carry out the impact test on the specimens using the drop test system, a fixture shown in Figure 5 was designed and fabricated. This fixture consisted of a fixed and a moving part. The test specimens were locked between these parts. After releasing the dropped weight, it stroked the moving part and a force was exerted on the specimens. A Dynatup 9250 HV (Instron, Norwood, MA, USA) drop tower was used to conduct the test. This machine is designed to raise a drop weight to the desired height and release it to strike the test specimen. The impact energy from the drop tower can be adjusted by changing either the impact velocity by the drop height or mass by the drop weight, as the equation for the kinetic energy prescribes: To carry out the impact test on the specimens using the drop test system, a fixture shown in Figure 5 was designed and fabricated. This fixture consisted of a fixed and a moving part. The test specimens were locked between these parts. After releasing the dropped weight, it stroked the moving part and a force was exerted on the specimens. performing resistance spot welds. The exact values of the current and force were measured using a Rogowski coil and piezoelectric load cell. According to AWS D8.9, the welding electrode was RWMA group A, Class 2, truncated cone nose, with a face diameter of 8 mm [27]. The welding parameters for preparing test specimens were selected based on some previous practical welding experiences using these types of material. The electrode force was adjusted to 5.7 kN and all welds were performed in 3 pulses. Since the aim was to achieve the maximum possible tensile strength of the welded joints, the selected parameters were at the acceptable range of weldability and mainly close to the expulsion condition. Representative cross-sections for both coated and uncoated sheets are shown in Figure 4 with a welding current of 8.2 kA applied over 9 cycles in 3 pulses.
(a) (b) To carry out the impact test on the specimens using the drop test system, a fixture shown in Figure 5 was designed and fabricated. This fixture consisted of a fixed and a moving part. The test specimens were locked between these parts. After releasing the dropped weight, it stroked the moving part and a force was exerted on the specimens. A Dynatup 9250 HV (Instron, Norwood, MA, USA) drop tower was used to conduct the test. This machine is designed to raise a drop weight to the desired height and release it to strike the test specimen. The impact energy from the drop tower can be adjusted by changing either the impact velocity by the drop height or mass by the drop weight, as the equation for the kinetic energy prescribes: A Dynatup 9250 HV (Instron, Norwood, MA, USA) drop tower was used to conduct the test. This machine is designed to raise a drop weight to the desired height and release it to strike the test specimen. The impact energy from the drop tower can be adjusted by changing either the impact velocity by the drop height or mass by the drop weight, as the equation for the kinetic energy prescribes: The drop tower and the fabricated fixture, positioned over the base of the system, is shown in Figure 6.
The drop tower and the fabricated fixture, positioned over the base of the system, is shown in Figure 6

Tensile Shear Failure Loads
The purpose of this study was to determine the suitable welding parameters required to achieve the highest tensile load capability of the welded joints. Hence, because of selecting most of the welding parameters near the expulsion condition, the number of specimens was limited and redundant tests were avoided. For both types of materials, seven tensile shear strength specimens with at least two repetitions were prepared by applying different combinations of welding current and time. The welding parameters are shown in Table 2. Among these seven selected welding parameters, four combinations were near the expulsion condition for achieving the maximum tensile shear failure load and the other three were relatively far from this condition to allow studying the effects of welding parameters on tensile shear peak load. The effects of welding current and time on the tensile shear failure load of welded joints for both types of steel were determined. The data are represented in Figure 7.

Tensile Shear Failure Loads
The purpose of this study was to determine the suitable welding parameters required to achieve the highest tensile load capability of the welded joints. Hence, because of selecting most of the welding parameters near the expulsion condition, the number of specimens was limited and redundant tests were avoided. For both types of materials, seven tensile shear strength specimens with at least two repetitions were prepared by applying different combinations of welding current and time. The welding parameters are shown in Table 2. Among these seven selected welding parameters, four combinations were near the expulsion condition for achieving the maximum tensile shear failure load and the other three were relatively far from this condition to allow studying the effects of welding parameters on tensile shear peak load. The effects of welding current and time on the tensile shear failure load of welded joints for both types of steel were determined. The data are represented in Figure 7. Because of the limited number of tests for each welding time, tensile peak load versus welding current for all of the welding times are shown in one graph. It is worth mentioning that all of the weldings were conducted in three pulses. In general, the uncoated specimens exhibited a higher tensile failure load than the Al-Si coated specimens. The maximum tensile failure load of the welded joint for the uncoated steel was 39.7 kN at 10 kA  Because of the limited number of tests for each welding time, tensile peak load versus welding current for all of the welding times are shown in one graph. It is worth mentioning that all of the weldings were conducted in three pulses. In general, the uncoated specimens exhibited a higher tensile failure load than the Al-Si coated specimens. The maximum tensile failure load of the welded joint for the uncoated steel was 39.7 kN at 10 kA welding current and 11 cycles/pulse welding time, while it was 33.0 kN for the Al-Si coated steel at 8.8 kA welding current and 13 cycles/pulse welding time. For both types of material, when the selected welding current was in low range the failure mode was the IF type. When the welding current increased, the strength of the joint improved and the failure mode changed to PO. These two failure modes, IF and PO, are shown in Figure 8. Because of the limited number of tests for each welding time, tensile peak load versus welding current for all of the welding times are shown in one graph. It is worth mentioning that all of the weldings were conducted in three pulses. In general, the uncoated specimens exhibited a higher tensile failure load than the Al-Si coated specimens. The maximum tensile failure load of the welded joint for the uncoated steel was 39.7 kN at 10 kA welding current and 11 cycles/pulse welding time, while it was 33.0 kN for the Al-Si coated steel at 8.8 kA welding current and 13 cycles/pulse welding time. For both types of material, when the selected welding current was in low range the failure mode was the IF type. When the welding current increased, the strength of the joint improved and the failure mode changed to PO. These two failure modes, IF and PO, are shown in Figure 8.

Failure Energy Absorption
The effects of the welding parameters on the failure energy absorption of the welded joints for both types of materials are reported in Figure 9. Similar to tensile failure load, the energy absorption of welded joints improved by increasing welding current at a welding time of nine cycles/pulse. When the selected welding parameters were near the expulsion condition, the value of energy absorption was acceptable. The maximum failure of energy absorption for the uncoated welded joint was 93.8 J at a 10 kA of welding current and 11 cycles/pulse of welding time, while it was 50.95 J for the Al-Si coated steel at 8.8 kA and 13 cycles/pulse of welding time.

Failure Energy Absorption
The effects of the welding parameters on the failure energy absorption of the welded joints for both types of materials are reported in Figure 9. Similar to tensile failure load, the energy absorption of welded joints improved by increasing welding current at a welding time of nine cycles/pulse. When the selected welding parameters were near the expulsion condition, the value of energy absorption was acceptable. The maximum failure of energy absorption for the uncoated welded joint was 93.8 J at a 10 kA of welding current and

Correlation of Nugget Diameter on Tensile Failure Load and Failure Energy Absorption
In general, weld nugget diameter is regarded as a criterion for the quality and strength of spot-welded joints. The effect of weld nugget diameter on the tensile failure load and energy absorption of the specimens is shown in Figure 10. It was observed that for the uncoated specimens with increasing nugget diameters of up to 8.5 mm, the tensile failure force and energy absorption increased and then, despite increasing nugget diameter, decreased. For the Al-Si coated specimens, by increasing weld nugget diameter the tensile failure and energy absorption increased.

Impact Test Results
For both types of sheets, five impact test specimens with at least two repetitions were prepared by applying different combinations of welding current and time near the expulsion condition for achieving the highest impact failure load. Impact tests were conducted on these specimens. The welding parameters are shown in Table 3. The effects of the welding parameters on the dynamic failure energy absorption of the welded joints for both types of materials are shown in Figure 11.

Correlation of Nugget Diameter on Tensile Failure Load and Failure Energy Absorption
In general, weld nugget diameter is regarded as a criterion for the quality and strength of spot-welded joints. The effect of weld nugget diameter on the tensile failure load and energy absorption of the specimens is shown in Figure 10. It was observed that for the uncoated specimens with increasing nugget diameters of up to 8.5 mm, the tensile failure force and energy absorption increased and then, despite increasing nugget diameter, decreased. For the Al-Si coated specimens, by increasing weld nugget diameter the tensile failure and energy absorption increased.

Correlation of Nugget Diameter on Tensile Failure Load and Failure Energy Absorption
In general, weld nugget diameter is regarded as a criterion for the quality and strength of spot-welded joints. The effect of weld nugget diameter on the tensile failure load and energy absorption of the specimens is shown in Figure 10. It was observed that for the uncoated specimens with increasing nugget diameters of up to 8.5 mm, the tensile failure force and energy absorption increased and then, despite increasing nugget diameter, decreased. For the Al-Si coated specimens, by increasing weld nugget diameter the tensile failure and energy absorption increased.

Impact Test Results
For both types of sheets, five impact test specimens with at least two repetitions were prepared by applying different combinations of welding current and time near the expulsion condition for achieving the highest impact failure load. Impact tests were conducted on these specimens. The welding parameters are shown in Table 3. The effects of the welding parameters on the dynamic failure energy absorption of the welded joints for both types of materials are shown in Figure 11.

Impact Test Results
For both types of sheets, five impact test specimens with at least two repetitions were prepared by applying different combinations of welding current and time near the expulsion condition for achieving the highest impact failure load. Impact tests were conducted on these specimens. The welding parameters are shown in Table 3. The effects of the welding parameters on the dynamic failure energy absorption of the welded joints for both types of materials are shown in Figure 11.  (a) (b) Figure 11. Dynamic failure energy absorption of welded joints during impact test versus welding parameters for (a) uncoated hot-Scheme 1500 and (b) Al-Si coated hot-stamped Usibor1500.
The purpose of this study was to determine the suitable welding parameters to achieve the maximum dynamic load capability of the welded joints. Hence, because of selecting the welding parameters near the expulsion condition, the number of specimens was limited and redundant tests were avoided. Because of the limited number of tests for each welding time, dynamic failure energy absorption versus welding current for all of the welding times are shown in one graph. It is worth mentioning that all of the weldings were conducted in three pulses. In general, the uncoated specimens exhibited a higher impact failure energy absorption than the Al-Si coated specimens. The maximum dynamic failure energy absorption for the uncoated welded joint was 280 J at 10.12 kA welding current and 13 cycles/pulse of welding time, while it was 232 J for Al-Si coated steel at 8.84 kA and 11 cycles/pulse of welding time. The effect of weld nugget diameter on dynamic failure energy absorption of the specimens is shown in Figure 12. It is observed that for both types of material, an increasing nugget diameter caused the dynamic failure energy absorption to increase. The purpose of this study was to determine the suitable welding parameters to achieve the maximum dynamic load capability of the welded joints. Hence, because of selecting the welding parameters near the expulsion condition, the number of specimens was limited and redundant tests were avoided. Because of the limited number of tests for each welding time, dynamic failure energy absorption versus welding current for all of the welding times are shown in one graph. It is worth mentioning that all of the weldings were conducted in three pulses. In general, the uncoated specimens exhibited a higher impact failure energy absorption than the Al-Si coated specimens. The maximum dynamic failure energy absorption for the uncoated welded joint was 280 J at 10.12 kA welding current and 13 cycles/pulse of welding time, while it was 232 J for Al-Si coated steel at 8.84 kA and 11 cycles/pulse of welding time. The effect of weld nugget diameter on dynamic failure energy absorption of the specimens is shown in Figure 12. It is observed that for both types of material, an increasing nugget diameter caused the dynamic failure energy absorption to increase.
The results show that the probability of IF fracture for Al-Si coated specimens is more than uncoated specimens. This phenomenon exhibited that the failure behavior of welded joints for Al-Si coated hot-stamped steel is worse than uncoated steel during impact forces such as crashes. The typical failure modes of specimens such as IF failure or PO failure after impact test are shown in Figure 13. The results show that the probability of IF fracture for Al-Si coated specimens is more than uncoated specimens. This phenomenon exhibited that the failure behavior of welded joints for Al-Si coated hot-stamped steel is worse than uncoated steel during impact forces such as crashes. The typical failure modes of specimens such as IF failure or PO failure after impact test are shown in Figure 13.

Effects of Al-Si Coating on Mechanical Behavior of Welded Joint
During the spot welding of hot-stamped Al-Si coated steels, the coating tends to melt due to the high temperature at the faying interface, and a large portion of the molten coating is displaced from under the electrodes and gathers around the weld nugget edges. Some portions of the coating remain on the molten and solidified area and create Al-Fe intermetallic phases. The presence of brittle Al-Fe phases in the weld nuggets causes a decrease in their strength. Figure 14a shows an optical image of the area around the welded zone. Figure 14b,c shows enlarged images of region "b" and "c", respectively. Because of aggregation of the molten Al-Si coating after weld solidification, the boundary of the weld nugget near the faying surfaces is weakly bonded. In addition, the presence of a notch creates a crack in the edge of the weld nugget, which is due to the concentration of stress in this area. The existence of molten Al-Si around the fusion zone may penetrate cracks through the fragile bonded area and spread along the fusion zone. Hence, in the case of Al-Si coated steel (compared to uncoated steel) the presence of brittle Al-Fe phases in the weld nuggets decreases the mechanical properties of the welded joints and causes a decrease in the maximum tensile failure load and energy absorption in both static and impact tests. Additionally, it increases the risk of changing failure mode from PO to IF fracture in these tests.  The results show that the probability of IF fracture for Al-Si coated specimens is more than uncoated specimens. This phenomenon exhibited that the failure behavior of welded joints for Al-Si coated hot-stamped steel is worse than uncoated steel during impact forces such as crashes. The typical failure modes of specimens such as IF failure or PO failure after impact test are shown in Figure 13.

Effects of Al-Si Coating on Mechanical Behavior of Welded Joint
During the spot welding of hot-stamped Al-Si coated steels, the coating tends to melt due to the high temperature at the faying interface, and a large portion of the molten coating is displaced from under the electrodes and gathers around the weld nugget edges. Some portions of the coating remain on the molten and solidified area and create Al-Fe intermetallic phases. The presence of brittle Al-Fe phases in the weld nuggets causes a decrease in their strength. Figure 14a shows an optical image of the area around the welded zone. Figure 14b,c shows enlarged images of region "b" and "c", respectively. Because of aggregation of the molten Al-Si coating after weld solidification, the boundary of the weld nugget near the faying surfaces is weakly bonded. In addition, the presence of a notch creates a crack in the edge of the weld nugget, which is due to the concentration of stress in this area. The existence of molten Al-Si around the fusion zone may penetrate cracks through the fragile bonded area and spread along the fusion zone. Hence, in the case of Al-Si coated steel (compared to uncoated steel) the presence of brittle Al-Fe phases in the weld nuggets decreases the mechanical properties of the welded joints and causes a decrease in the maximum tensile failure load and energy absorption in both static and impact tests. Additionally, it increases the risk of changing failure mode from PO to IF fracture in these tests.

Effects of Al-Si Coating on Mechanical Behavior of Welded Joint
During the spot welding of hot-stamped Al-Si coated steels, the coating tends to melt due to the high temperature at the faying interface, and a large portion of the molten coating is displaced from under the electrodes and gathers around the weld nugget edges. Some portions of the coating remain on the molten and solidified area and create Al-Fe intermetallic phases. The presence of brittle Al-Fe phases in the weld nuggets causes a decrease in their strength. Figure 14a shows an optical image of the area around the welded zone. Figure 14b,c shows enlarged images of region "b" and "c", respectively. Because of aggregation of the molten Al-Si coating after weld solidification, the boundary of the weld nugget near the faying surfaces is weakly bonded. In addition, the presence of a notch creates a crack in the edge of the weld nugget, which is due to the concentration of stress in this area. The existence of molten Al-Si around the fusion zone may penetrate cracks through the fragile bonded area and spread along the fusion zone. Hence, in the case of Al-Si coated steel (compared to uncoated steel) the presence of brittle Al-Fe phases in the weld nuggets decreases the mechanical properties of the welded joints and causes a decrease in the maximum tensile failure load and energy absorption in both static and impact tests. Additionally, it increases the risk of changing failure mode from PO to IF fracture in these tests.

Conclusions
The effects of Al-Si coating on the static and dynamic tensile shear strength of RSW joints of hot-stamped steels were studied. From this experimental research, the conclusions are as follows:


The static tensile shear failure load of RSW joints of coated and uncoated steels increases with an increasing welding current and time;  After RSW of hot-stamped Al-Si coated steels, the coating tends to melt and create Al-Fe intermetallic phases at the welding zone which causes a decrease in the welded joint strength;  Because of the aggregation of molten Al-Si in the edge of the weld nugget, the static tensile failure load and dynamic failure energy absorption of Al-Si coated steel is lower than uncoated steel, and the risk of changing failure mode from Po to IF increases in dynamic tests;  The maximum tensile shear failure load of welded joints for uncoated steel is 39.7 kN while it is 33.0 kN for Al-Si coated steel;  The maximum dynamic failure energy absorption obtained for welded joints of uncoated steel is 280 J, while it is 232 J for Al-Si coated steel;  Due to a lower tensile shear failure capacity, failure energy absorption, and high probability of IF failure for Al-Si coated, the tensile strength behavior of welded joints is worse for Al-Si coated hot-stamped steel than uncoated steel.

Conclusions
The effects of Al-Si coating on the static and dynamic tensile shear strength of RSW joints of hot-stamped steels were studied. From this experimental research, the conclusions are as follows:

•
The static tensile shear failure load of RSW joints of coated and uncoated steels increases with an increasing welding current and time; • After RSW of hot-stamped Al-Si coated steels, the coating tends to melt and create Al-Fe intermetallic phases at the welding zone which causes a decrease in the welded joint strength; • Because of the aggregation of molten Al-Si in the edge of the weld nugget, the static tensile failure load and dynamic failure energy absorption of Al-Si coated steel is lower than uncoated steel, and the risk of changing failure mode from Po to IF increases in dynamic tests; • The maximum tensile shear failure load of welded joints for uncoated steel is 39.7 kN while it is 33.0 kN for Al-Si coated steel; • The maximum dynamic failure energy absorption obtained for welded joints of uncoated steel is 280 J, while it is 232 J for Al-Si coated steel; • Due to a lower tensile shear failure capacity, failure energy absorption, and high probability of IF failure for Al-Si coated, the tensile strength behavior of welded joints is worse for Al-Si coated hot-stamped steel than uncoated steel.