Advances in Materials Science and Engineering

Advances in Materials Science and Engineering / 2016 / Article

Research Article | Open Access

Volume 2016 |Article ID 2509734 | https://doi.org/10.1155/2016/2509734

A. R. Sufizadeh, S. A. A. Akbari Mousavi, "Metallurgical and Mechanical Research on Dissimilar Electron Beam Welding of AISI 316L and AISI 4340", Advances in Materials Science and Engineering, vol. 2016, Article ID 2509734, 11 pages, 2016. https://doi.org/10.1155/2016/2509734

Metallurgical and Mechanical Research on Dissimilar Electron Beam Welding of AISI 316L and AISI 4340

Academic Editor: Jörg M. K. Wiezorek
Received20 Jun 2016
Revised01 Sep 2016
Accepted19 Sep 2016
Published16 Oct 2016

Abstract

Dissimilar electron beam welding of 316L austenitic stainless steel and AISI 4340 low alloy high strength steel has been studied. Studies are focused on effect of beam current on weld geometry, optical and scanning electron microscopy, X-ray diffraction of the weld microstructures, and heat affected zone. The results showed that the increase of beam current led to increasing depths and widths of the welds. The optimum beam current was 2.8 mA which shows full penetration with minimum width. The cooling rates were calculated for optimum sample by measuring secondary dendrite arm space and the results show that high cooling rates lead to austenitic microstructure. Moreover, the metallography result shows the columnar and equiaxed austenitic microstructures in weld zone. A comparison of HAZ widths depicts the wider HAZ in the 316L side. The tensile tests results showed that the optimum sample fractured from base metal in AISI 316L side with the UTS values is much greater than the other samples. Moreover, the fractography study presents the weld cross sections with dimples resembling ductile fracture. The hardness results showed that the increase of the beam current led to the formation of a wide softening zone as HAZ in AISI 4340 side.

1. Introduction

It is evident that deployment of dissimilar metals plays the most important part of construction processes due to the technological advances of production in the industry. Dissimilar joints would improve not only products quality in terms of cost but also design and enhancement of the structures’ stability. The intrinsic properties of the materials used in dissimilar welding play a major role in determining the weld quality [1].

Electron beam welding is one of the widely used welding methods for joining dissimilar materials in industries. The primary advantage of electron beam welding is its high depth to width ratio which results in a very strong weld. The quality of weld depends upon the parameters, namely, accelerating voltage, beam current, welding speed, focus current, and vacuum level [2].

Electron beam welding has high power density and consequently led to small heat affected zone and high heating and cooling rates. The spot size of the EBW can vary between 0.2 mm and 13 mm, though only smaller sizes are used for welding. The depth of penetration is proportional to the amount of power supplied but is also dependent on the location of the focal point. Penetration is maximized when the focal point is slightly below the surface of the work piece [3].

The AISI 4340 stainless steel is of those high strength low alloy steels that their strengths are achieved with appropriate heat treatments [4]. It has good weld ability and is usually welded by the GTAW process [5].

Resistance welding and many other arc welding processes are used to weld austenitic stainless steels. But the resistance to corrosion and cracking in austenitic stainless steels are the major problems where careful selection on welding process or any other further solution is required. The corrosion properties of AISI 316L stainless steel are enhanced by addition of molybdenum. The AISI 316L stainless steel microstructure contains austenite with a little ferrite [6].

Basically, in dissimilar welding, the degree of dilution of each material in the weld bead is very important. This matter is also one of the influential parameters in the weld microstructures in the laser welding process [7]. The degree of dilution of the weld can be achieved by adjusting beam-focal point position relative to the joint interface of the weld. There is a possibility that the beam diameter is deviated away from the interface during laser welding in practice. Positioning of the focused beam by CNC facilitates location control and chemical compositions of the weld. This procedure requires close tolerances during the preparation of the joint [8].

Arivazhagan et al. studied the microstructure and mechanical properties of AISI 304 stainless steel and AISI 4140 low alloy steel joints by electron beam welding (EBW). The yield strengths of weldments performed by EBW were higher than those carried out by GTAW. In the weldments performed by EBW, the failures occurred on the HAZ of the AISI 4140 steels [9].

The fatigue performance of an electron-beam welded joint between AISI 4140 and AISI 316L steel has been investigated by Çalik et al. Results indicated that a good strength weld can be achieved between the two dissimilar steels by electron beam welding with a fatigue limit approaching 190 MPa, which is a value between the fatigue limits of the base materials. The microstructure of the electron-beam welded dissimilar AISI 4140-AISI 316L joint consisted of both columnar and equiaxed austenite grains in the weld interface [10].

2. Research Method

In this study, welding was performed with the electron beam welding machine. Table 1 shows the chemical compositions of the AISI 4340 low alloy high strength steel and AISI 316L austenitic stainless steel obtained by wave dispersive X-ray fluorescence spectroscopy. Table 2 presents the mechanical properties of base metals.


Material elementsSiPSCMoMnNiCrFe

AISI 316L0.390.0310.0050.0272.891.8410.6516.6268.9519.912.38
AISI 43400.350.0100.0010.3910.210.791.900.8874.791.4413.99


AlloyUltimate tensile strength (MPa)Yield strength (MPa)Elongation%

AISI 316L51519045
AISI 434074447522

Figures 1(a) and 1(b) depict the microstructures of the AISI 316L stainless steel and the AISI 4340 steel. The typical picture of the welded sample is shown in Figure 1(c) in which a butt square weld joint was used. The thickness of the base metals at the joint cross section was 0.5 mm. No filler metal was used for electron beam welding and the welding was performed autogenously.

In order to investigate the effects of EBW parameters on the weld microstructures, the welding tests were (conducted) carried out with selected welding parameters according to Table 3.


Sample numberVoltage, KVWeld focus value, AmpsBeam current, , mAVacuum, TorrSpeed, cm/s

145 KV2.2 A1.6 mA0.2 cm/s
245 KV2.2 A2.2 mA0.2 cm/s
345 KV2.2 A2.8 mA0.2 cm/s
445 KV2.2 A3.4 mA0.2 cm/s
545 KV2.2 A4.0 mA0.2 cm/s

The chemical etching was performed for optical examinations with the solution containing 40 mL methanol, 20 mL choleric acid, and 15 mL HNO3 for 40 seconds. The electrochemical etching was carried out for SEM examinations with 6 V voltage and NaOH solution in 20 seconds. Also in order to reveal the microstructure and phases, the optical and scanning electron microscopy and X-ray diffraction were implemented.

The EDS analysis was carried out to investigate the variations (in weight%) of the main chemical elements across the weld cross section.

The tensile tests were carried out according to ASTM E8 for subsize specimen [11]. Figures 2(a) and 2(b) show the schematic dimensions of tensile test specimen and typical tensile test welded sample, respectively.

The Vickers microhardness was carried out with applying 100 gr load in 15 seconds. The microhardness profiles were obtained across the 316L stainless steel, the weld zone, and the 4340 steel. Figure 3 shows the schematic of the microhardness points investigated across the welding zone.

3. Results and Discussion

3.1. The Effects of Beam Current on Weld Properties
3.1.1. The Effects of Beam Current on Weld Geometry

Beam current is one of the most vital parameters in the electron beam welding process. Experiments have been conducted to note its effects on the depth of penetration.

Trials were conducted, to determine the range of beam current that can be used for a thickness of 0.5 mm. Hence, the range of beam currents is determined to be in between 1.6 mA and 4 mA. At constant voltage, weld focus value, speed of 0.2 cm/min, duration, and vacuum, beam current was varied as tabulated in Table 3 and observations were made.

According to previous investigation [12], the heat input was directly increased with beam current. The results were shown in Figure 4. The depth and width of the weld were increased with beam current. The width of the weld is more influential to the beam current than the depth of the weld (see Figure 4). The maximum depth was obtained for 2.8, 3.4, and 4 mA and was full penetration weld with 500 μm depths. The maximum width for the 4 mA beam current was 1950 μm. In equal weld depths, the beam current increase could cause the excessive increase of weld widths which is not desirable in such low heat input process. Therefore, sample number 3 (2.8 mA) was selected as the optimum one, since the penetration of all three samples (2.8, 3.4, and 4 mA) is the same.

3.1.2. The Effects of Beam Current on Weld Microstructure

Based on Figure 5, fine grained austenitic microstructures are seen as the dissimilar weld microstructure. The electron beam welding parameters play important role on weld microstructure and mechanical properties due to their effect on heat input. The effects of beam current on weld grain size were investigated.

Figure 5 shows that the weld grain size increases with beam current. The reason can be attributed to the increase of power and heat input [13] which reduces the cooling rate. Therefore, there is enough time for excessive grain growth in the weldment solidification period. Moreover, according to Figure 6, the observation showed that increasing the beam current values more than 2.8 mA led to significant grain growth rate but in lower beam current values the gradual growth was accrued. The reason can be attributed to the excessive increase of beam current only which led to increase in weld volume and decrease in cooling rate. At this condition, there is much more time for growth stage during solidification.

3.2. The Microhardness Tests of the Welded Specimen

Figure 7 shows the microhardness profiles. The -axis in Figure 7 shows the locations where microhardness tests were carried out. These locations are shown in Figure 3.

According to Figure 7, if the austenitic weld microstructure is formed, the magnitude of the weld microhardness will be between those of base metals (450–550 HV). On the other hand, the microhardness of the weld zone is greater than that of the AISI 316L stainless steel base metal due to producing fine grain austenitic weld microstructure. The microhardness of the weld zone is lower than that of the AISI 4340 steel base metal because the austenitic weld microstructure is softer than the martensitic structure of the AISI 4340 steel base metal. The fluctuation of hardness profile in weld center line is the result of the change of solidification mode from columnar dendrite to equiaxed dendrite by transition from fusion line to center line according to Figure 16.

In the HAZ near AISI 316L stainless steel side, the hardness is similar to base metal. However, on the other side (near the AISI 4340 steel) the softened zone is observed. The reason can be attributed to producing coarse grained softening zone in the HAZ near the fusion boundary, according to Figure 17(b). The minimum hardness occurred on HAZ sample number 5. This is attributed to the beam current value in this sample which is the highest among all samples. So the heat affected zone was much longer exposed to high temperature and wider softening zones were created.

3.3. The Tensile Tests of the Welded Samples

The engineering stress-engineering strain curves obtained by the tensile tests of the transverse welded full penetration samples (numbers 3, 4, and 5) are shown in Figure 8. According to the results of the tensile tests, samples number 3 (optimum depth/width ratio) and number 4 fractured above 515 MPa (the ultimate tensile strength of the AISI 316L stainless steel). On the other hand, it was observed that the strength magnitude of EBW-welded samples was lower than that of the AISI 4340 steel and higher than that of the AISI 316L stainless steel. These results were confirmed with the effect of producing fine grained microstructure in the austenitic weld zone. Figure 9 shows the fracture locations in the samples. Samples numbers 3 and 4 fractured in the AISI 316L stainless steel sides while sample number 5 was fractured on HAZ in side of AISI 4340. The reason for low tensile strength for sample number 5 can be described. The beam current of sample number 5 is the highest value so that the wide softening zone in HAZ was created. The failure occurred in the softening zone in heat affected zone. These results are in good agreement with the hardness results of the HAZ in AISI 4340 side, shown in Figure 7.

Figure 10 shows the fractography analysis obtained by SEM. The dimples in Figures 10(a) and 10(b) verified the ductile fracture behavior of AISI 316L as the base metal in samples numbers 3 and 4. Moreover, the dimples on Figure 10(c) shows ductile fracture behavior of AISI 4340 as the HAZ in sample number 5.

3.4. The Microstructure Investigations

Considering the results obtained at previous sections, one may conclude that the optimum parameters were applied on sample number 3 from mechanical properties and weld geometry point of view. Therefore, in this section the metallurgical properties, solidification patterns, and the microstructure of sample number 3 were studied.

3.4.1. The Microstructure Prediction by Schaeffler Diagram

The dissimilar weld microstructures prediction of Schaeffler diagram (Figure 11) with those achieved by the experiments had been investigated by the EDS analyses of Cr, Ni, Mn, C, Si, and Mo elements for the points shown in Figure 12. The EDS results were used to calculate Cr and Ni equivalent content for all three regions considered (Table 4).


Sample locationPredicted microstructureActual microstructure

Assumption
dilution (50%)
11.213.2A + MA
Figure 12(d) (near 4340)8.112.8MA
Figure 12(b) (near 316L)17.810.6A + M + FA
Figure 12(c) (weld center)15.511.3A + MA

According to the Schaeffler diagram (see Figure 11), the austenite + martensite microstructures of are predicted; however, Figure 12 shows that the full austenitic microstructure is produced in the weld microstructures. The reason can be attributed to high cooling rate in EBW process which causes changes in the solidification mode from ferritic to austenitic mode according to Figure 13(a) [14]. The results of Figure 12 are in good agreement with previous investigations [15, 16].

3.4.2. The Calculation of Welding Cooling Rate

In order to study the cooling rate of sample number 3, the measurement of secondary dendritic arm space (SDAS) was carried out. According to the investigation of [17], the following formula was explained for the relationship between SDAS and cooling rate:where is cooling rate (K/s) and and are material constants which are approximately 100 and 0.5 for austenitic microstructure [17]. Table 5 shows the results of and cooling rate measurements. The results reveal that, based on the high cooling rate (816 K/s), referring to Figure 13(a), the austenite dendrite tip temperature is higher than ferrite and this attributed to change solidification mode from austenite + martensite to fully austenite. High cooling rate effect is in accordance with formation of austenitic microstructures in Figure 13(b), which is also in accordance with the pervious investigations [15, 16].


DAS (µm)SDAS (µm)SDA thickness (µm)Cooling rate (K/s)

5.993.50.8816

3.4.3. The Microsegregation in Dendritic Microstructure

In the next step, the EDS analyses for sample number 3 were carried out in order to investigate the microsegregation during solidification and differences of percent of alloys element in subgrain, dendrites, and interdendritic spaces were done. The results were shown in Figure 14 and Table 6. According to Table 6 at point A (subgrain boundary), the percent of ferrite promotion such as Cr and Mo was 13.39% and 3.23%, respectively, while in the matrix and point B that element percent was reduced to 10.38% and 1.75%, respectively.


Element⁢Weight percent of elements (%)
ABCD

Silicon0.440.660.30.6
Chromium13.3910.3811.3312.26
Manganese0.770.110.010.01
Nickel7.255.927.616.03
Molybdenum3.231.751.842.55

These characterizations are the consequence of the austenite dendrites growth during solidification and also the reduction of the solubility of ferrite promotions elements such as Cr and Mo. In this process, the austenitic former elements are concentrating on the dendritic structures and the ferritic former elements are traveling to interdendritic structures. In order to investigate ferrite formation in interdendritic spaces, the XRD test (Figure 15) was carried out. The results show that no ferrite phases were created and the microstructure is completely austenite. This result is in accordance with Figures 12 and 13, which is also conforming to the previous investigations [15, 16].

According to the EDS results (Table 7), the secondary dendritic arm space (SDAS) shows that the microsegregation was less than dendritic arm space (DAS) and the percent of Cr and Mo was 12.24% and 2.54%, respectively. The smaller diffusion zone, solute redistribution of elements in dendrite tips, and very high cooling rate are the major factors resulting in formation of SDAS and so the reduction of microsegregation in SDAS.


ElementWeight percent (%) at point EWeight percent (%) at point F

Silicon0.40.5
Chromium19.516.4
Manganese0.80.9
Nickel7.110.5
Molybdenum2.92.2

3.4.4. The Solidification Mode in the Weld Zone

According to Figure 16, transitions from fusion line to center line lead to changing the microstructure of weld from columnar dendrites to equiaxed dendrites. These results were attributed to the low growth rate () in the fusion boundary and it increases from the fusion boundary to the weld centerline. On the other hand, the thermal gradient () is minimum in the weld center and maximum in the fusion boundary. Therefore, the / ratio which determines the solidification mode of the microstructure is maximum in the fusion boundary and minimum in the weld center line. Therefore, the microstructure is columnar dendrite in the fusion boundary which changes to equiaxed dendrite structure by reducing the ratio in the center of the weld. This change attributed to fluctuation of hardness in weld center line on the microhardness diagram in Figure 7.

3.5. The Heat Affected Zone (HAZ) Microstructure

According to Figure 17(a), the close zone near fusion line formation of new phase was detected in HAZ area on AISI 316L side. Two phenomena would probably occur: the formation of Cr carbide and ferrite. In this zone attributed to low percent of carbon, the probability of Cr carbide formation was too low which is in accordance with the results of EDS analyzes depicted in Table 7 with no formation of Cr carbide. However, according to the EDS results in Figure 18 and Table 7, the increase in amount of Cr in white zone comparison with matrix (in Figure 18) will increase the probability of formation of ferrite phase in grain zone. On the other hand, the absence of grain growth in HAZ (the lock austenite grain boundaries by ferrite) makes this phenomenon more feasible and probable.

In order to investigate formation of ferrite phase, the XRD test was done (Figure 19). The results show little percent ferrite was created. This result strengthens the possibility of the formation of ferrite phase in white zone according to Figure 18.

According to Figure 17, the HAZ widths are different in the AISI 316L and AISI 4340 sides, 50 and 10 μm, respectively. The reason was due to using different materials with different heat conduction coefficients and also due to performing various heat inputs. Based on Figure 17, the HAZ width in AISI 316L stainless steel side was 3 or 4 times greater than that of AISI 4340 steel side. The major reason is attributed to the different heat conduction coefficients of AISI 316L stainless steel and AISI 4340 steel. The heat conduction coefficients were 44.5 and 16.3 W/m·K for AISI 4340 steel and AISI 316L stainless steel, respectively. In fact, the heat conduction coefficient of AISI 4340 is approximately 3 times greater than that of AISI 316L stainless steel. Therefore, the heat input induced in the materials leads to producing smaller HAZ size in the AISI 4340 steel side than the HAZ size in the AISI 316 stainless steel side.

Figure 17(b) shows the heat affected zone on AISI 4340 base metal side. The small narrow zone with approximately 10 μm width containing large grains was detected close to fusion line. This attributed to low heat input in electron beam welding process. The softening zone in this sample was too small and can be ignored. These results were in accordance with microhardness results in Figure 7. Moreover according to Figure 17(c), the HAZ width in AISI 4340 side for sample number 5 was 45 μm. The softening zone with coarse microstructure was detected which is in accordance with microhardness results (Figure 7) and tensile test results (Figures 8, 9, and 10). This could be attributed to high beam current value in sample number 5 as was explained in Sections 3.1.1 and 3.1.2.

4. Conclusions

This paper presents electron beam welding of AISI 316L stainless steel and AISI 4340 low alloy steel. The welding process was carried out by changing the beam current values from 1.6 mA to 4 mA. The depth and width of the weld were increased with beam current. The full penetration weld with 500 μm depth was obtained at 2.8, 3.4, and 4 mA. The microhardness values of weld zone were greater than that in the AISI 316L stainless steel due to fine grain austenitic formation in weld microstructure. In the HAZ near the AISI 4340 steel, the softening zone was observed. The tensile tests results showed that samples 3 and 4 fractured from base metal in AISI 316L side with the UTS values much greater than the UTS values of sample number 5 which fractured from HAZ in AISI 4340 side due to high beam current value and wide softening zone occurred in sample number 5. The full austenitic microstructure was produced in the weld zone. The SDAS measurements showed the high cooling rate during the process. Such cooling rate is in accordance with the formation of austenitic microstructure. The low heat input resulted in formation of small HAZ and the absence of Cr carbide. The study showed that the HAZ width in the AISI 316L stainless steel side was 3 or 4 times greater than that of the AISI 4340 side. The optimum beam current was obtained at 2.8 mA.

Competing Interests

The authors declare that there are no competing interests regarding the publication of this paper.

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Copyright © 2016 A. R. Sufizadeh and S. A. A. Akbari Mousavi. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.


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