GMAW of Dissimilar AHSS Sheets

GMAW of Dissimilar AHSS Sheets

Arc Welding

This is a summary of a paper of the same title, authored by K. Májlinger, E. Kalácska, and P. Russo Spena, used by permission.M-65

 

Researchers at the Budapest University of Technology and Economics and the Free University of Bozen-Bolzano tested gas metal arc welding (GMAW) of dissimilar Advanced High-Strength Steel (AHSS) sheets.M-65 The test pieces were 100 x 50 mm samples of 1.4 mm TWIP (TWIP1000) and 0.9 mm TRIP (HCTC800T) sheet steels were welded in a lap joint configuration with 0.8 mm diameter AWS ER307Si austenitic stainless steel wire to determine appropriate GMAW parameters for good quality welds. Quality was determined by external appearance, microstructure, and mechanical properties. Good welds were achieved with linear heat inputs (Q) with ranges from 500-650 kJ/m. The only fractures that occurred appeared within the weld bead by ductile failure modes. The HAZ of the TWIP steel showed grain coarsening and the HAZ of the TRIP steel experienced microstructural changes relative to the distance from the fusion boundary. The ultimate tensile strength (UTS) varies between 73%-84% of the weaker of the two steels.

Welding was conducted with an automated linear drive system with pure Argon (99.996% Ar) shielding gas at 10L/min. Wire feed rates were approximately 3.5 m/min with Direct Current Electrode Positive (DCEP) polarity. Changes in current, voltage, weld speed, and the resulting linear energy are compared in Table 1.

Figure 1: Overview of Dissimilar AHSS GMAW Welding.M-65

Figure 1: Overview of Dissimilar AHSS GMAW Welding.M-65

 

Table 1: Results of the preliminary welding tests in terms of TWIP-TRIP joint quality.M-65

Table 1: Results of the preliminary welding tests in terms of TWIP-TRIP joint quality.M-65

 

After welding, transverse sections were cut from the welds and etched to show the microstructure. Vickers hardness testing was conducted on the weld samples based on the ASTM E384 standard. Tensile tests were performed on the samples according to the EN ISO 6892-1 standard. Tests were also conducted on unwelded TWIP and TRIP steels for comparison. Scanning electron microscopy (SEM) examinations were made of fracture surfaces to determine failure modes and examine for microscopic weld defects.

The study concluded that dissimilar welds between AHSS steels with the GMAW process can be achieved with consistent results desired for automotive applications.

Figure 2: Vickers Hardness Across Weldment.M-65

Figure 2: Vickers Hardness Across Weldment.M-65

 

Figure 3: Ductile Failure in FZ.M-65

Figure 3: Ductile Failure in the fragile zones (FZ).M-65

 

 

Transformation Induced Plasticity (TRIP)

Transformation Induced Plasticity (TRIP)

1stGen AHSS, 3rdGen AHSS, AHSS, Steel Grades

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Metallurgy

The microstructure of Transformation Induced Plasticity (TRIP) steels contains a matrix of ferrite, with retained austenite, martensite, and bainite present in varying amounts. Production of TRIP steels typically requires the use of an isothermal hold at an intermediate temperature, which produces some bainite. Higher silicon and carbon content of TRIP steels result in significant volume fractions of retained austenite in the final microstructure. Figure 1 shows a schematic of TRIP steel microstructure, with Figure 2 showing a micrograph of an actual sample of TRIP steel. Figure 3 compares the engineering stress-strain curve for HSLA steel to a TRIP steel curve of similar yield strength.

 

Figure 1: Schematic of a TRIP steel microstructure showing a matrix of ferrite, with martensite, bainite and retained austenite as the additional phases.

Figure 1: Schematic of a TRIP steel microstructure showing a matrix of ferrite, with martensite, bainite and retained austenite as the additional phases.

 

Figure 2: Micrograph of Transformation Induced Plasticity steel.

Figure 2: Micrograph of Transformation Induced Plasticity steel.

 

Figure 3: A comparison of stress strain curves for mild steel, HSLA 350/450, and TRIP 350/600.K-1

Figure 3: A comparison of stress strain curves for mild steel, HSLA 350/450, and TRIP 350/600.K-1

 

 

During deformation, the dispersion of hard second phases in soft ferrite creates a high work hardening rate, as observed in the DP steels. However, in TRIP steels the retained austenite also progressively transforms to martensite with increasing strain, thereby increasing the work hardening rate at higher strain levels. This is known as the TRIP Effect. This is illustrated in Figure 4, which compares the engineering stress-strain behavior of HSLA, DP and TRIP steels of nominally the same yield strength. The TRIP steel has a lower initial work hardening rate than the DP steel, but the hardening rate persists at higher strains where work hardening of the DP begins to diminish. Additional engineering and true stress-strain curves for TRIP steel grades are shown in Figure 5.

 

Figure 4: TRIP 350/600 with a greater total elongation than DP 350/600 and HSLA 350/450 Reference K-1

Figure 4: TRIP 350/600 with a greater total elongation than DP 350/600 and HSLA 350/450. K-1

 

Figure 5: Engineering stress-strain (left graphic) and true stress-strain (right graphic) curves for a series of TRIP steel grades. Sheet thickness: TRIP 350/600 = 1.2mm, TRIP 450/700 = 1.5mm, TRIP 500/750 = 2.0mm, and Mild Steel = approx. 1.9mm. V-1

Figure 5: Engineering stress-strain (left graphic) and true stress-strain (right graphic) curves for a series of TRIP steel grades. Sheet thickness: TRIP 350/600 = 1.2mm, TRIP 450/700 = 1.5mm, TRIP 500/750 = 2.0mm, and Mild Steel = approx. 1.9mm. V-1

 

 

The strain hardening response of TRIP steels are substantially higher than for conventional HSS, resulting in significantly improved formability in stretch deformation. This response is indicated by a comparison of the n-value for the grades. The improvement in stretch formability is particularly useful when designers take advantage of the improved strain hardening response to design a part utilizing the as-formed mechanical properties. High n-value persists to higher strains in TRIP steels, providing a slight advantage over DP in the most severe stretch forming applications.

Austenite is a higher temperature phase and is not stable at room temperature under equilibrium conditions. Along with a specific thermal cycle, carbon content greater than that used in DP steels are needed in TRIP steels to promote room-temperature stabilization of austenite. Retained austenite is the term given to the austenitic phase that is stable at room temperature.

Higher contents of silicon and/or aluminum accelerate the ferrite/bainite formation. These elements assist in maintaining the necessary carbon content within the retained austenite. Suppressing the carbide precipitation during bainitic transformation appears to be crucial for TRIP steels. Silicon and aluminum are used to avoid carbide precipitation in the bainite region.

The carbon level of the TRIP alloy alters the strain level at which the TRIP Effect  occurs. The strain level at which retained austenite begins to transform to martensite is controlled by adjusting the carbon content. At lower carbon levels, retained austenite begins to transform almost immediately upon deformation, increasing the work hardening rate and formability during the stamping process. At higher carbon contents, retained austenite is more stable and begins to transform only at strain levels beyond those produced during forming. At these carbon levels, retained austenite transforms to martensite during subsequent deformation, such as a crash event.

TRIP steels therefore can be engineered to provide excellent formability for manufacturing complex AHSS parts or to exhibit high strain hardening during crash deformation resulting in excellent crash energy absorption.

The additional alloying requirements of TRIP steels degrade their resistance spot-welding behavior. This can be addressed through weld cycle modification, such as the use of pulsating welding or dilution welding.  Table 1 provides a list of current production grades of TRIP steels and example automotive applications:

Table 1: Current Production Grades Of TRIP Steels And Example Automotive Applications.

Table 1: Current Production Grades Of TRIP Steels And Example Automotive Applications.

 

Some of the specifications describing uncoated cold rolled 1st Generation transformation induced plasticity (TRIP) steel are included below, with the grades typically listed in order of increasing minimum tensile strength and ductility. Different specifications may exist which describe hot or cold rolled, uncoated or coated, or steels of different strengths. Many automakers have proprietary specifications which encompass their requirements.
• ASTM A1088, with the terms Transformation induced plasticity (TRIP) steel Grades 690T/410Y and 780T/440YA-22
• JFS A2001, with the terms JSC590T and JSC780TJ-23
• EN 10338, with the terms HCT690T and HCT780TD-18
• VDA 239-100, with the terms CR400Y690T-TR and CR450Y780T-TRV-3
• SAE J2745, with terms Transformation Induced Plasticity (TRIP) 590T/380Y, 690T/400Y, and 780T/420YS-18

 

Transformation Induced Plasticity Effect

Austenite is not stable at room temperature under equilibrium conditions. An austenitic microstructure is retained at room temperature with the combined use of a specific chemistry and controlled thermal cycle. Deformation from sheet forming provides the necessary energy to allow the crystallographic structure to change from austenite to martensite. There is insufficient time and temperature for substantial diffusion of carbon to occur from carbon-rich austenite, which results in a high-carbon (high strength) martensite after transformation. Transformation to high strength martensite continues as deformation increases, as long as retained austenite is still available to be transformed.

Alloys capable of the TRIP effect are characterized by a high ductility – high strength combination. Such alloys include 1st Gen AHSS TRIP steels, as well as several 3rd Gen AHSS grades like TRIP-Assisted Bainitic Ferrite, Carbide Free Bainite, and Quench & Partition Steels.

 

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RSW Parameter Guidelines

RSW Parameter Guidelines

Resistance Spot Welding

 

Parameter Guidelines

In summary, Tables 1 and 2 provide the AWS C1.1 Spot Welding Parameter Guidelines link to Recommended Practices for Resistance Welding. These general guidelines can be used to approximate which parameters can be used to begin the Resistance Spot Welding (RSW) process of a specific part thickness. From the recommended parameters, changes can be made on a specific stack-up to ensure an acceptable strength and nugget size for a particular application. Additionally, more complicated RSW parameter guidelines using a pulsation welding schedule with AC 60 Hz for welding AHSS is included in Table 3.

Table 1: Spot welding parameters for low-carbon steel 350-700 MPa (AHSS).A-14

Table 1: Spot welding parameters for low-carbon steel 350-700 MPa (AHSS).A-14

  1. Use of coated parameters recommended with the presence of a coating at any faying surface.
  2. These recommendations are based on available weld schedules representing recommendations from resistance welding equipment suppliers and users.
  3. For intermediate thicknesses parameters may be interpolated.
  4. Minimum weld button shear strength determined as follows:
    • ST = (-6.36E-7 × S2 + 6.58E-4 × S + 1.674) × S × 4 t1.5)/1000
    • ST = Shear Tension Strength (kN)
    • S = BM Tensile Strength (MPa)
    • t = Material Thickness (mm)
  5. Metal thicknesses represent the actual thickness of the sheets being welded. In the case of welding two sheets of different thicknesses, use the welding parameters for the thinner sheet.
  6. Welding parameters are applicable when using electrode materials included in RWMA Classes 1 , 2, and 20.
  7. Electrode shapes listed include: A-pointed, B-domed, E-truncated, F-radiused. Figure 2 shows these shapes.
    • The use of Type-B geometry may require a reduction in current and may result in excessive indentation unless face is dressed to specified diameter.
    • The use of Type F geometry may require an increase in current.
  8. Welding parameters are based on single-phase AC 60 Hz equipment.
  9. Nugget diameters are listed as:
    • Minimum diameter that is recommended to be considered a satisfactory weld.
    • Initial aim setup nugget diameter that is recommended in setting up a weld station to produce nuggets that consistently surpass the satisfactory weld nugget diameter for a given number of production welds.

 

"Table

Table 2: Spot welding parameters for low-carbon steel >700 MPa (AHSS). A-14

  1. Use of coated parameters recommended with the presence of a coating at any faying surface.
  2. These recommendations are based on available weld schedules representing recommendations from resistance welding equipment suppliers and users.
  3. For intermediate thicknesses parameters may be interpolated.
  4. Minimum weld button shear strength determined as follows:
    • ST = (-6.36E-7 × S2 + 6.58E-4 × S + 1.674) × S × 4 t1.5)/1000
    • ST = Shear Tension Strength (kN)
    • S = BM Tensile Strength (MPa)
    • t = Material Thickness (mm)
  5. Metal thicknesses represent the actual thickness of the sheets being welded. In the case of welding two sheets of different thicknesses, use the welding parameters for the thinner sheet.
  6. Welding parameters are applicable when using electrode materials included in RWMA Classes 1, 2, and 20.
  7. Electrode shapes listed include: A-pointed, B-domed, E-truncated, F-radiused. Figure 2 shows these shapes.
    • The use of Type-B geometry may require a reduction in current and may result in excessive indentation unless face is dressed to specified diameter.
    • The use of Type F geometry may require an increase in current.
  8. Welding parameters are based on single-phase AC 60 Hz equipment.
  9. Nugget diameters are listed as:
    • Minimum diameter that is recommended to be considered a satisfactory weld.
    • Initial aim setup nugget diameter that is recommended in setting up a weld station to produce nuggets that consistently surpass the satisfactory weld nugget diameter for a given number of production welds.

 

Table 3: AHSS bare-to-bare, bare-to-galvanized, Galvanized-to-galvanized RSW parameters for pulsating AC 60 Hz.

Table 3: AHSS bare-to-bare, bare-to-galvanized, Galvanized-to-galvanized RSW parameters for pulsating AC 60 Hz.A-14

 

 

Heat, Material and Thickness Balances

The heat input in Resistance Spot Welding (RSW) is defined as:

Heat Input = I2Rt

where: I is welding current
R is total resistance, and
t is weld time

The heat input must be changed depending on the gauge and grade of the steel. Compared to low strength steel at a particular gauge, the AHSS at the same gauge will need less current. Similarly, the thin gauge material needs less current than thick gauge. Controlling the heat input according to the gauge and grade is called heat balance in RSW.

For constant thickness, Table 1 shows steel classification based on strength level. With increasing group numbers, higher electrode force, longer weld time, and lower current are required for satisfactory RSW. Material combinations with one group difference can be welded with little or no changes in weld parameters. Difference of two or three groups may require special considerations in terms of electrode cap size, force, or type of power source.

 

Table 1: Steel classification for RSW purposes.A-11

Table 1: Steel classification for RSW purposes.A-11

 

For a particular steel grade, changes in thickness may require adoption of special schedules to control heat balance. When material type and gauge are varied together, specific weld schedules may need to be developed. Due to the higher resistivity of AHSS, the nugget growth occurs preferentially in AHSS. Electrode life on the AHSS-side may be reduced due to higher temperature on this side. In general, electrode life when welding AHSS may be similar to mild steel because of lower operating current requirement due to higher bulk resistivity in AHSS. This increase in electrode life may be offset in production due to poor part fit up created by higher AHSS springback. Frequent tip dressing will maintain the electrode tip shape and help achieve consistently acceptable quality welds.

 

 

Welding Current Mode

AHSS can be welded with power sources operated with either AC or DC types (Figure 1). Middle-Frequency Direct-Current (MFDC) has an advantage over conventional AC due to both unidirectional and continuous current. These characteristics assist in controlling and directing the heat generation at the interface. Current mode has no significant difference in weld quality. It should be noted that both AC and DC can easily produce acceptable welds where thickness ratios are less than 2:1. However, some advantage may be gained using DC where thickness ratios are over 2:1, but welding practices must be developed to optimize the advantages. It also has been observed that nugget sizes are statistically somewhat larger when using DC welding with the same secondary weld parameters than with AC. Some studies have shown that welding with MFDC provides improvements in heat balance and weld process robustness when there is a thickness differential in AHSS (as shown in Figure 2). DC power sources have been reported to provide better power factors and lower power consumption than AC power sources. Specifically, it has been reported that AC requires about 10% higher energy than DC to make the same size weld.L-7

 

 

Figure 1: Range for 1.4-mm DP 350/600 CR steel at different current modes with a single pulse.L-2

Figure 1: Range for 1.4-mm DP 350/600 CR steel at different current modes with a single pulse.L-2

 

Figure 2: Effect of current mode on dissimilar-thickness stack-upL-2

Figure 2: Effect of current mode on dissimilar-thickness stack-up.L-2

 

Consult safety requirements for your area when considering MFDC welding for manual weld gun applications. The primary feed to the transformers contains frequencies and voltages higher than for AC welding.

 

 

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RSW of Advanced High-Strength Steels

RSW of Advanced High-Strength Steels

Resistance Spot Welding

In general, if any type of AHSS [Dual-Phase (DP), Transformation-Induced Plasticity (TRIP), Complex Phase (CP), Ferrite Bainite (FB), or Martensitic (MS)] is used for the first time, the user should take the welding schedules applied to mild steel and then:

  • Increase the electrode force by 20% or more depending on Yield Strength.
  • Increase weld time as appropriate.

If these changes are insufficient, try these additional changes:

  • A multi-pulse welding schedule (several pulses or post heating).
  • Larger tip diameter and/or change the type of electrode.
  • Increase the minimum weld size.

When resistance welded, AHSS require less current than conventional mild steel or HSLA because AHSS have higher electrical resistivity. Therefore, current levels for AHSS are not increased and may even need to be reduced depending on material chemical composition. However, most AHSS grades may require higher electrode forces for equivalent thickness of mild steels because electrode force depends on material strength. If thick mild steel or HSLA steel (of the same thickness) is replaced by an equivalent thickness of AHSS, the same forces may be required during assembly welding.

AHSS often have tighter weld windows (welding parameters that give acceptable welds) when compared to mild steels, as shown in the Figure 1.

Figure 1: Schematic weld lobes for AHSS, HSLA, and mild steel with a shift to lower currents with increased strength.

Figure 1: Schematic weld lobes for AHSS, HSLA, and mild steel with a shift to lower currents with increased strength.

The current range (kA) for AHSS of 600-1400MPa during RSW is shown in Figures 2 and 3. The process window for Resistance Spot Welding of AHSS is influenced by the electrode force and welding time used in a major way. The current range increases by an average of 500 A for every additional 500 N of electrode force (Figure 2). The current range also increases by an average of 250 A for each additional 40 ms of welding time (Figure 3). Extra amounts of electrode force and welding time lead to increased current range, allowing for a wider process window.

Figure 2: RSW with AHSS, current range for varying electrode force (Cap Type B 16/6, 6-mm tip diameter, single pulse, 340-ms weld time, 250-ms hold time, plug failures.).I-6

Figure 2: RSW with AHSS, current range for varying electrode force (Cap Type B 16/6, 6-mm tip diameter, single pulse, 340-ms weld time, 250-ms hold time, plug failures.).I-6

 

Figure 3: RSW with AHSS, current range for varying weld time (Cap Type B 16/6, 6-mm tip diameter, single pulse, 3.5-kN electrode force, 250-ms hold time, plug failures.).O-1

Figure 3: RSW with AHSS, current range for varying weld time (Cap Type B 16/6, 6-mm tip diameter, single pulse, 3.5-kN electrode force, 250-ms hold time, plug failures.).O-1

A more extensive weld studyT-5 of three DP HDGA (45/45 g/m2) coated steels showed similar welding behavior for all three steels. The 1.6-mm-thick steels were DP 340/590, DP 420/780, and DP 550/980. To characterize the welding behavior of the steels, useful current ranges and static weld tensile tests were performed. The useful current range is the difference between the welding current required to produce a minimum button size (Imin) and the current that causes expulsion of weld metal (Imax). In this study, the 4√t as the minimum button diameter was used, where “t” is the nominal sheet thickness. This is generally used in the automotive and steel industries. The weld current range was 2.2 kA for the DP 340/590 and DP 420/780 and 2.5 kA for the DP 550/980 steel (Figure 4). These current ranges are sufficiently wide to weld successfully the DP steels. The study also found no weld imperfections, which means these three DP steels are weldable with simple, easy to use welding parameters.

Figure 4: Welding current ranges for 1.6-mm DP HDGA steels with minimum tensile strengths of 590, 780, and 980 MPa.T-5

Figure 4: Welding current ranges for 1.6-mm DP HDGA steels with minimum tensile strengths of 590, 780, and 980 MPa.T-5

 

Average reported weld hardness was 380 HV (Vickers Hardness) for the DP 340/590 and 415 HV for the other two. Again, all three DP steels had similar weld hardness distributions. The study also concluded that weld fracture mode alone is not a good indicator of weld integrity and performance. The load to fracture should be considered more important in judging weld integrity.

A second studyT-6 compared two 1.6-mm-thick HDGA (45/45 g/m2) steels: DP 420/700 and TRIP 420/700. The weld current range for 18 cycles weld time was similar: 1.4 kA for the DP 420/700 and 1.5 kA for the TRIP 420/700. The average weld hardness was 400 HV for both steels. The study concluded that acceptable welds with no imperfections can be produced in both steel grades. Both steel grades are readily weldable with easily adoptable welding parameters. Weld tensile strength differences between the two steels were small and not considered statistically significant.

Weld schedules (Figure 5) with pulsed current profiles for AHSS can have weld-current ranges similar to mild steel. Even though there is no increased tendency for weld expulsion with AHSS avoiding weld expulsion is highly desirable with AHSS. Loss of nugget material can affect weld-nugget size and strength.

Figure 5: Schematics of optimized weld schedules for AHSS

Figure 5: Schematics of optimized weld schedules for AHSS.B-1

 

Post annealing (tempering pulse weld schedule) of TRIP steel may alter weld fracture mode and weld current range (Figure 6). However, since studies have shown that the occurrence of partial or IF fractures does not necessarily indicate poor weld quality, the use of pulsed current is not required to improve weld quality. Further, the effect of current pulsing on tensile and fatigue properties, as well as the electrode tip life, is not known. Therefore, users should perform their own evaluations regarding the suitability of such modified parameters.

Figure 6: Post annealing may enlarge weld current range.B-1

Figure 6: Post annealing may enlarge weld current range.B-1

Additional work using Quench and Partition (Q&P) 980 showed less current required than conventional steels because it has higher electrical resistivity. Due to ultra-high base metal (BM) strength, it needs higher electrode force than conventional steels which have equivalent thickness. The weld lobe of 1.6-mm Q&P 980 is shown in Figure 7 with the pulsed weld time and force of 5.8 kN. The yellow zone of this figure shows the fracture mode of full button (FBF) when peel tested. Some pictures of these weld spots’ fracture mode are captured in Figure 8, for diameters of 6.0 to 7.7 mm.

Figure 7: Pulsed current profile and weld lobe of 1_6-mm Q&P 980.B-4

Figure 7: Pulsed current profile and weld lobe of 1_6-mm Q&P 980.B-4

 

Figure 8: Fracture mode of weld spots in yellow zone. B-4

Figure 8: Fracture mode of weld spots in yellow zone.B-4

 

Hardness measurements and cross sections through the spot weld different zones can be identified as depicted in Figure 9. In a first step, the spot-welded joint can be subdivided into three zones: weld, Heat Affected Zone (HAZ), and BM. The weld is covered by the HAZ, where the melting temperature is not reached but high enough to change the microstructure. This region is dominated by inhomogeneous properties due to the different temperature and cooling gradients. Considering the hardness measurements of AHSS 3 sample, even a softening in the HAZ compared to the BM can be observed. Finally, the HAZ is surrounded by the BM, which does not show any local changes within the structure. These modifications of microstructure in the HAZ and weld are essential for the load-bearing capacity because the strength and ductility are drastically changed in comparison to the BM. Normally a high hardness is related to high strength and less ductility.

Figure 9: Hardness distribution through spot welds of various strength steels.P-7

Figure 9: Hardness distribution through spot welds of various strength steels.P-7

Weld spot micrograph and microhardness of 1.6-mm Q&P 980 is shown in Figure 10, in which no weld defects, such as cracks, shrinkage void, pore, no fusion, deep indentation, etc. were found. Hardness testing is typically performed as shown in Figure 11 (diagonal traverse across the weld from BM of top coupon to BM of bottom coupon) using a suitable instrument for micro-indentation hardness testing (Vickers or Knoop).

 

Figure 10: Weld spot micrograph and microhardness of 1.6-mm DP 980. B-4

Figure 10: Weld spot micrograph and microhardness of 1.6-mm DP 980.B-4

 

Figure 11: Typical cross-sectioned weld and hardness traverse.A-13

Figure 11: Typical cross-sectioned weld and hardness traverse.A-13

The different hardness values seen in a typical cross-sectioned weld depict different microstructural regions.P-8  Figure 12 shows the temperature distribution of a typical 2T weldment of hot stamped boron steel. At the solidified weld nugget, we see the highest temperatures and steadily decrease toward the unaffected base metal. The weld metal, coarse grain heat affected zone, fine grain heat affected zone, and unaffected base metal are made up of martensitic microstructure. The base metal has this microstructure due to the heat treatment (hot stamping) process. The weld metal, coarse grain heat affected zone, and fine grain heat affected zone are exposed to austenitizing temperature upon welding and are cooled rapidly reforming the martensite microstructure. The subcritical heat affected zone has a unique microstructure of over-tempered martensite. In this region, the peak temperature re below the Ac1, causing the base metal martensitic microstructure to decompose into ferrite and cementite. Micrographs of the different weld regions can be seen in Figure 13.

Figure 12: Temperature distribution of a typical 2T RSW of hot stamped boron steel.P-8

Figure 12: Temperature distribution of a typical 2T RSW of hot stamped boron steel.P-8

 

Figure 13: Different microstructures seen throughout the HAZ of a 2T hot stamped boron steel joint.P-8

Figure 13: Different microstructures seen throughout the HAZ of a 2T hot stamped boron steel joint.P-8

Steel Grades

Steel Grades

Steel Grades

See the brief Tutorial on using the Steel Grades search.

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Transformation Induced Plasticity (TRIP), , , , , , , , , , , , , , , , , , , , , 1stgen-steel 3rd-generation ahss astm-a1088 bainite en-10338 ferrite jfs-a2001 martensite microstructure retained-austenite sae-j2745 strain-hardening-exponent transformation-induced-plasticity trip trip-effect trip-metallurgy vda-239-100 work-hardening1stgen-ahss 3rdgen-ahss ahss steel-grades metallurgy
Complex Phase, , , , , , , , , , , , , , , , , , , 1stgen-steel ahss astm-a1088 bainite bendability bending complex-phase cp en-10338 ferrite local-formability martensite microalloy microstructural-components microstructure precipitation-strengthening retained-austenite vda-239-1001stgen-ahss ahss steel-grades metallurgy
Ferrite-Bainite, , , , , , , , , , , , , , , , , , , , , 1stgen-steel ahss bainite cut-edge-stretching edge-stretchability en-10338 fb ferrite ferrite-bainite hhe hole-expansion hole-extrusion hole-flanging hot-rolled-steel jfs-a2001 microstructural-components microstructure stretchability stretching vda-239-1001stgen-ahss ahss steel-grades metallurgy
Ultra-Low Carbon (DDS – EDDS), , , , , , , , , , , , dds deep-drawing-steel edds extra-deep-drawing-steel ferrite ferrite-ultra-low-carbon-mild-steel microstructure mild-steel ulc ultra-low-carbon vacuum-degassed vd-iflower-strength-steels steel-grades metallurgy
3rd Generation Steels, , , , , , , , , , , , , , , , , , , , , , , , 3rd-gen advanced-high-strength-steels ahss carbide-free-bainite cfb ch complex-phase-high-ductility cp-hd dh downgauging dp-hd dual-phase-high-ductility high-ductility intercritical-anneal manganese medium-mn overaging qp quench-and-partition tbf third-generation trip-assisted-bainitic-ferrite trip-effect3rdgen-ahss ahss steel-grades metallurgy
Carbon-Manganese (CMn), , , , , , , , , , , , , astm-a1008m c-mn carbon carbon-and-manganese carbon-manganese cmn conventional-high-strength-steel high-strength-steel jfs-a2001 jis-g3135 manganese structural-steel yield-strengthconventional-h-s-s steel-grades metallurgy
High Strength Low Alloy Steel, , , , , , , , , , , , , , , , astm astm-a1008m c-mn carbon-manganese cmn conventional-high-strength-steel en-10268 high-strength-low-alloy hsla jfs-a2001 jis-g3135 la microalloy precipitation-strengthening vda-239-100 yield-strengthconventional-h-s-s steel-grades metallurgy
Mild Steels, , , , , , , , , , , , , , , , , astm-a1008m dq dqak dqsk draw-quality-steel drawing-steel ds en-10130 ferrite jfs-a2001 jis-g3141 low-carbon microstructure mild-steel ulc ultra-low-carbon vda-239-100lower-strength-steels steel-grades metallurgy
Interstitial-Free High Strength, , , , , , , , , , , edds en-10268 if if-hs if-rephos interstitial-free-high-strength jfs-a2001 rephosphorized ulc vd-if vda-239-100conventional-h-s-s steel-grades metallurgy
Bake Hardenable, , , , , , , , , , , , , , , , , , , , , , astm-a1008m bake-hardenability bake-hardenable bake-hardening bake-hardening-effect baking-index bh bh-effect bhi carbon dent dislocations en10268 jfs-a2001 jis-g3135 microstructural-components paint-bake sae-j2575 strain-aging vda239-100 work-hardeningahss conventional-h-s-s steel-grades metallurgy
Twinning Induced Plasticity, , , , , , , , , , , , , , 2nd-gen ahss dynamic-strain-aging fe-mn manganese microstructure plc-effect portevin-lechatelier-effect strain-rate-sensitivity stretch-formability twinning-induced-plasticity twip twip4eu2ndgen-ahss ahss steel-grades metallurgy