# Effect of Electrode Types on the Solidification Cracking Susceptibility of Austenitic Stainless Steel Weld Metal

Authors: J. U. Anaele; O. O. Onyemaobi; C. S. Nwobodo; C. C. Ugwuegbu
Journal: International Journal of Metals
 (2015)

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## Abstract

The effect of electrode types on the solidification cracking susceptibility of austenitic stainless steel weld metal was studied. Manual metal arc welding method was used to produce the joints with the tungsten inert gas welding serving as the control. Metallographic and chemical analyses of the fusion zones of the joints were conducted. Results indicate that weldments produced from E 308-16 (rutile coated), E 308-16(lime-titania coated) electrodes, and TIG welded joints fall within the range of1.5≤Creq./Nieq.≤1.9 and solidified with a duplex mode and were found to be resistant to solidification cracking. The E 308-16 weld metal had the greatest resistance to solidification cracking. Joints produced from E 310-16 had Creq./Nieq. ratio < 1.5 and solidified with austenite mode. It was found to be susceptible to solidification cracking. E 312-16 produced joints having Creq./Nieq. ratio > 1.9 and solidified with ferrite mode. It had a low resistance to solidification cracking.


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## Body

## 1. Introduction

Stainless steel is a common name for steel alloys that consist of 10.5 weight percent or more of chromium (Cr) and more than 50 weight percent of iron (Fe). Stainless steels may be classified by their crystalline structure into three main types: austenitic, ferritic, and martensitic stainless steel. Austenitic stainless steel (ASS) contains a maximum of 0.15 percent carbon, a minimum of 16 percent chromium, and sufficient nickel and/or manganese to retain an austenitic structure at all temperatures from the cryogenic temperature to the melting point of the alloy.Austenitic stainless steels have become the most widely used stainless steels and correspond to about 70 percent of all the stainless steel produced worldwide, as a result of their mechanical and metallurgical properties and their good weldability [1]. The excellent properties of ASS which include high tensile strength, good impact resistance, excellent ductility, corrosion, and wear resistances have found various applications in domestic as well as in many engineering industries, some of which are cooking utensils, food processing equipment, equipment for chemical industry, truck trailers, kitchen sinks, exterior architecture, pressure boilers and vessels, fossil-fired power plant, fuel gas desulphurization equipment, evaporator tubing, super heater and reheating tubing, steam headers, and pipes, among others [2].In recent times, advancement has been made in such joining process as adhesives, mechanical fasteners, brazing, and soldering. However, welding remains the most important metal joining process, even as arc welding is the most widely used fusion-welding process. In the fabrication of austenitic stainless steel components, welding is one of the most employed methods [3, 4]. Despite the good weldability property exhibited by ASS, hot cracking has been the major metallurgical problem encountered during welding of austenitic stainless steel components. It is caused by the formation of low melting eutectics at the grain boundaries during welding, which cause failure under the action of shrinkage stresses associated with solidification. Solidification cracking is a type of hot cracking which depends on mechanical restraint and metallurgical susceptibility [5]. It consists of fractures at the interdendritic and/or intergranular weld metal boundaries in the solidification process, during which the liquid phase of the mushy melt becomes rich in impurities, mainly sulphur (S), and phosphorus (P). This phenomenon reduces the mechanical strength at the grain and dendritic boundaries, rendering them susceptible to cracking and failure eventually [6]. One of such failures is the corrosion cracking of a grade 304 stainless steel pipe improperly seam welded and meant for the conveyance of glucose solution in Illinois USA [7].In view of the problem of solidification cracking in ASS weldment, many works have been carried out in order to explain the phenomenon of solidification cracking and ways of preventing it. As early as 1941, Scherer et al. found that crack resistance in ASS weld metal may be improved by adjusting the composition to 5–35 percent ferrite in the completed weld. Hull [8] confirmed this by stating that when ferrite content in the completed weld increases beyond 35 weight percent, the weld metal would become susceptible to solidification cracking, but the mechanism by which crack resistance is achieved by the effect of retained ferrite in the weld metal is still not completely understood.Good attempts, however, have been made to explain the effect. Borland and Younger [9] suggested that the higher solubility for impurity elements in delta ferrite leads to less interdendritic segregation and reduces cracking tendency. Thier et al. [10] found that the volume contraction associated with ferrite-austenite transformation reduces tensile stresses close to the crack tip, which decreases cracking tendency. Apart from the effect of retained delta ferrite in the control of solidification cracking in ASS weldment, Baldev et al. [5] and Borland [11] suggested that solidification cracking in ASS weld metal could be minimized by the various practices which reduce mechanical restraint in the completed weld metal. As can be seen in some of the research works cited above, solidification cracking in austenitic stainless steel weldment is partly a function of the weld metal composition. A well designed product, for example, can fail by cracking if the weld rod selected results in the weld zone having lower alloy content than that of the parent metal. Therefore, there is need to determine how the electrode type affects the solidification cracking susceptibility of ASS weldments. The main aim of this work is, therefore, to investigate the effect of electrode types on the microstructural susceptibility of the austenitic stainless steel weldment to solidification cracking.


## 2. Material and Methods

The base metal of the test specimens used for this study was type 304H austenitic stainless steel and the nominal chemical composition of the material is shown in Table1.Table 1
Chemical composition (wt.%) of the austenitic stainless steel material.
Element
wt.%
C
0.0570
Cr
18.5500
Ni
8.7200
Si
0.4400
Mn
1.7200
S
0.0075
P
0.0230
Mo
1.7200
Al
0.0057
Cu
0.2010
Co
0.1110
Nb
0.0270
V
0.0750
B
0.0022
Sn
0.0086
As
0.0870
Ca
0.0004
Fe
69.8000Two methods of welding were adopted, namely, Shielded Metal Arc Welding (SMAW) and Tungsten Inert Gas (TIG) Welding. The welding operations were conducted under constant condition as shown in Table2.Table 2
Welding parameters held constant in the welding operation.
Welding parameters
Tungsten inert gas welding
Manual metal arc welding
Welding current
110 A
110 A
Welding speed∗
60 mm/min.
60 mm/min.
Voltage
40 V
40 V
Polarity
DC electrode negative
DC electrode negative
Heat source
Arc
Arc
Weld pool shield
Argon gas
Electrode flux
Filler rod
304 H stainless steel wire
Welding electrode
Argon gas pressure
10 bars
—
∗Since the welding process was carried out manually, the welding speed is approximate and represents the average values.The variable parameter in this study was the welding electrodes while the welded joints produced from TIG autogenous welding served as the control or reference for comparism. The chemical composition of the electrodes, according to American Welding Society (AWS) electrode classification, is shown in Table3. The joints produced were subjected to metallographic test and chemical analysis.Table 3
Chemical composition of the electrodes.
Elements (wt.%)
E 308-16 (rutile coated) Electrodes (10 & 12)
E 308-16 (lime-titania) Electrode
E 310-16 Electrode
E 312-16 Electrode
C
0.08
0.08
0.08–0.12
0.15
Mn
0.7–2.0
0.5–2.5
1.0–2.5
0.7–2.0
Si
0.3–0.85
0.9
0.3–0.7
0.3–0.9
Cr
18–21
18–21
25–28
28–32
Ni
9–11
9–11
20–22
8–10.5
S
0.03
—
0.03
0.03
P
0.03
—
0.03
0.03
Mo
0.5
—
0.5
0.75
Cu
0.75
—
0.75
0.75


## 3. Results and Discussion

### 3.1. Metallographic Analysis of the Weldments

The results obtained from the metallographic test conducted on the Fusion Zone of the each weldment were analyzed.


#### 3.1.1. Analysis of E 312-16/10 Micrograph

The micrograph of E 312-16/10 fusion zone test specimen shown in Figure1 revealed a primary ferrite (dark) matrix containing secondary austenite (white) and carbide precipitation at the grain boundaries. The ferrite dendrites being the first to solidify had a lathy morphology and partly transforms into austenite after solidification by diffusion controlled mechanism.Figure 1
Fusion zone micrograph of E 312-16/10 welded joint.


#### 3.1.2. Analysis of E 310-16/10 Micrograph

E 310-16/10 fusion zone micrograph is shown in Figure2. As can be seen from the micrograph, the primary austenite (white) formed directly from the liquid as a primary dendritic phase as well as a secondary phase around ferrite. The interdendritic ferrite (dark) had a vermicular morphology engulfed in the austenite matrix, with carbide precipitation along the grain boundaries.Figure 2
Fusion zone micrograph of E 310-16/10 welded joint.


#### 3.1.3. Analysis of E 308-16/12 (Lime-Titania) Micrograph

Fu et al. [12] noted that ferrite-austenite (FA) solidification duplex mode is characterized by the formation of primary ferrite plus three phase (ferrite, austenite, and liquid) reactions at the terminal solidification stage. The fusion zone micrograph of E 308-16/12 (lime-titania) joint shown in Figure 3 revealed a plenty of fine colonies of lathy ferrite (dark) embedded in austenite (white) matrix. The result was a duplex microstructure consisting of thin lathy ferrite and austenite.Figure 3
Fusion zone micrograph of E 308-16/12 (lime-titania) welded joint.


#### 3.1.4. Analysis of TIG Micrograph

The fusion zone micrograph of TIG joint specimen shown in Figure4 revealed primary equiaxed dendritic and lathy ferrite (dark) enclosed in austenite (white) matrix, with the precipitation of carbides along grain boundaries.Figure 4
Fusion zone micrograph of TIG welded joint.


#### 3.1.5. Analysis of E 308-16/12 (Rutile) Micrograph

The E 308-16/12 (rutile) weld joint micrograph is shown in Figure5. The figure revealed a duplex structure of ferrite and austenite. The primary ferrite (dark) dendrites having a combination of lathy and vermicular ferrite morphology contained in austenite (white) matrix and a precipitation of carbide along grain boundaries. The amount of retained ferrite in E 308-16/12 (rutile) weld metal was found to be less than TIG and E 308-16/12 (lime-titania) weld metals, respectively, but more than that observed in E 308-16/10 (rutile) weld metal.Figure 5
Fusion zone micrograph of E 308-16/12 (rutile) welded joint.


#### 3.1.6. Analysis of E 308-16/10 (Rutile) Micrograph

The fusion zone micrograph of the E 308-16/10 (rutile) joint shown in Figure6 revealed a duplex structure consisting of ferrite (dark) and austenite (white). The primary ferrite had a thin lathy morphology engulfed by austenite which grew epitaxially and fills the interdendritic region of the primary ferrite. Carbide precipitation was also observed along the grain boundaries.Figure 6
Fusion zone micrograph of E 308-16/10 (rutile) welded joint.


### 3.2. Effect of Electrode Types on the Solidification Mode of Austenitic Stainless Steel Weld Metal

The results displayed in Table4 showed that the type of electrode selected in the welding of 304H stainless steel component affects the solidification microstructure of the weld metal. It was found that the TIG autogenous weld (Figure 4) had nearly the same solidification microstructure (FA) with the parent material (Figure 7), a result which was highly anticipated since there was no filler dilution in the completed weld as the tungsten electrode was nonconsumable. Weldments produced from E 308-16/12 (rutile), E 308-16/10 (rutile), and E 308-16/12 (lime-titania) electrodes had a duplex structure of ferrite-austenite (FA) with more or less amount of retained ferrite. Filler rod or electrode dilution is believed to be responsible for the evolved microstructure and solidification mode as shown in the results of the fusion zones micrographs of the E 308-16/12 (lime-titania), E 308-16/12 (rutile), and E 308-16/10 (rutile) joints displayed in Figures 3, 5, and 6, respectively. Joints produced from E 310-16/10 electrode (Figure 2) had austenite solidification mode whereas the joints made from E 312-16/10 (Figure 1) solidified with a primary ferrite solidification mode. The compromise reached between the parent material composition and filler rod or electrode dilution was found to be the major factor which determined the weld metal final microstructure and solidification mode. The findings of this research were found to be in line with the results of many researchers [5, 6, 12–15].Table 4
Values of Creq., Nieq., Creq./Nieq. ratio, and (P + S) wt.% of the tested weld joints.
Weld joints
Cr
eq.
Ni
eq.
Creq./Nieq.
(P + S) wt.%
Ferrite number (FN)
Solidification mode
E 308-16/12(rutile)weld joint
17.3019
9.7480
1.7750
0.0171
6
Ferrite-austenite (FA)
E 308-16/10(rutile)weld joint
17.2042
9.8678
1.7435
0.0094
5-6
Ferrite-austenite (FA)
E 308-16/12 (lime-titania) joint
19.8223
11.3915
1.7401
0.0086
10
Ferrite-austenite (FA)
E 310-16/10 weld joint
24.0273
22.7530
1.0560
0.0150
0-1
Austenite (A)
E 312-16/10 weld joint
26.8069
12.9698
2.0669
0.0140
50–55
Ferrite (F)
TIG weld joint
18.6387
10.9375
1.7041
0.0068Figure 7
Micrograph of the unwelded parent material.


### 3.3. Effect of Electrode Types on Weld Metal Composition and Cracking Propensity

The results of chemical analysis (presented in Table5) carried out on the weldments showed that electrode types have effect on the weld metal composition. The TIG autogenous weldment had nearly the same composition and Chromium-Nickel equivalence as that of the unwelded parent metal. However, remarkable difference in weld metal constitution was observed in the joints produced from the various electrodes relative to the Chromium-Nickel equivalence of the parent material. The Chromium-Nickel equivalence results, calculated for each weld joints and presented in Table 4, were obtained by using the the 1992 Welding Research Council model equation culled from Kotecki and Siewert [16]:(1)Creq.=Cr+Mo+0.7NbNieq.=Ni+35C+20N+0.25Cu,where, Creq. = Chromium equivalent and Nieq. = Nickel equivalent.Table 5
Chemical composition of the weld joints.
Elements wt.%
E 308-16/12 (rutile) weld
E 308-16/10 (rutile) weld
E 308-16/12 (lime-titania) weld
E 310-16/10 weld
E 312-16/10 weld
TIG weld
Carbon, C
0.0710
0.0730
0.0740
0.1350
0.0920
0.0600
Silicon, S
0.6900
0.6300
0.4900
0.5100
0.9100
0.3760
Manganese, Mn
1.2200
1.1800
1.3900
1.8700
1.3200
1.6200
Phosphorus, P
0.0061
0.0010
0.0010
0.0010
0.0010
0.0022
Sulphur, S
0.0110
0.0084
0.0076
0.0140
0.0130
0.0046
Chromium, Cr
17.1500
17.0200
19.5700
23.8500
26.7100
18.4500
Nickel, Ni
7.1900
7.2100
8.7400
17.9900
9.7300
8.7900
Molybdenum, Mo
0.1330
0.1660
0.2320
0.1570
0.0640
0.1740
Aluminium, Al
0.0055
0.0049
0.0056
0.0170
0.0072
0.0055
Copper, Cu
0.2920
0.4110
0.2460
0.1520
0.0790
0.1900
Cobalt, Co
0.0830
0.0960
0.1120
0.0770
0.0640
0.1170
Titanium, Ti
0.0240
0.0190
0.0110
0.4250
0.0160
0.0010
Niobium, Nb
0.0270
0.0260
0.0290
0.0290
0.0470
0.0210
Vanadium, V
0.0680
0.0700
0.1050
0.1080
0.1190
0.0770
Tungsten, W
0.0100
0.0100
0.0100
0.0100
0.0100
0.0560
Lead, Pb
0.0034
0.0030
0.0030
0.0030
0.0030
0.0038
Boron, B
0.0021
0.0018
0.0016
0.0017
0.0012
0.0022
Tin, Sn
0.0100
0.0098
0.0090
0.0075
0.0110
0.0110
Arsenic, As
0.0860
0.0810
0.0930
0.0960
0.1160
0.0950
Bismuth, Bi
0.0015
0.0015
0.0015
0.0015
0.0015
0.0015
Calcium, Ca
0.0002
0.0002
0.0003
0.0024
0.0003
0.0003
Iron, Fe
72.9000
73.0000
68.9000
54.6000
60.7000
69.9000The results showed that solidification cracking of the weld joints was sensitive toCreq./Nieq. ratio and solidification mode of the welds. E 308-16/12 (lime-titania), TIG, E 308-16/12 (rutile), and E 308-16/10 (rutile) welds with primary ferrite-austenite solidification modes and 1.5<Creq./Nieq.<1.9 are immune to solidification cracking in the order of decreasing resistance to solidification cracking, respectively. E 312-16/10 weld with ferrite solidification mode and Creq./Nieq.>1.9 has low susceptibility to solidification cracking, whilst E 310-16/10 weld with primary austenite solidification mode, Creq./Nieq.<1.5, and (P + S) wt.% = 0.015 may be susceptible to solidification cracking. Filler rod or electrode dilution is one of the factors which determined the final weld metal composition and solidification mode. Since solidification cracking is sensitive to weld metal composition and solidification mode, it therefore follows that the type of electrode used during welding of ASS materials determines the weld metal solidification cracking propensity.These results were compared with the cracking susceptibility of 300 series stainless steel based on Cr-Ni equivalence according to Hammar and Svensson [17] and found to be consistent and also in line with the findings of Arantes and Trevisan [6], Baldev et al. [5], Korinko and Malene [18], and Brooks and Thompson [19] who affirmed that the propensity for solidification cracking in austenitic stainless steel is sensitive to the Creq./Nieq. ratio, (P + S) wt.%, and ferrite number of the weld metal and maintained that weld metal with solidified FA mode in the range of 1.5<Creq./Nieq.<1.9 is immune to solidification cracking, while those in the region of Creq./Nieq.>1.9 and Creq./Nieq.<1.5 have low resistance and susceptible to solidification cracking, respectively. Generally, it was found that (P + S) wt.% values were less than 0.02 in the final composition of the respective welded joints, which is below the critical level suggested by Arantes and Trevisan [6], necessary to induce cracking.The results also suggest that the type of electrode coating has effect on the weld metal properties. The electrodes used for the welding were designated “-16” which denotes rutile coating for stainless steel electrodes. Rutile coatings are titania-type based electrodes containing little proportion of other additives. However, E 308-16/12 (lime-titania) electrodes were coated with titanium calcium and contain lime which makes it distinct from the rutile category. The presence of lime (which is a slag former) in E 308-16/12 (lime-titania) electrode was relevant in slowing down the cooling rate of both the weld pool and the just solidified weld metal of the resultant weldment. This suggests the reason for the slight difference observed in properties (such as ductility and strain hardening exponent) of weldments produced from the E 308-16 (lime titania) with respect to E 308-16 (rutile) welding electrodes. Consequently, the weldment produced from E 308-16/12 (lime-titania) electrode has a higher ductility of about 36% (in terms of percentage elongation) compared to 26% and 18% obtained from weldments produced from E 308-16/10 (rutile) and E 308-16/12 (rutile) electrodes, respectively. This result is confirmed in the micrograph of E 308-16/12 (lime-titania) weldment which suggests that the ferrite dendrite had more time for growth in the region where delta ferrite is most stable (due to slower cooling rate offered by lime in the electrode coating) compared to the micrographs of E 308-16/10 (rutile) and E 308-16/12 (rutile) weldments.


## 3.1. Metallographic Analysis of the Weldments

The results obtained from the metallographic test conducted on the Fusion Zone of the each weldment were analyzed.


### 3.1.1. Analysis of E 312-16/10 Micrograph

The micrograph of E 312-16/10 fusion zone test specimen shown in Figure1 revealed a primary ferrite (dark) matrix containing secondary austenite (white) and carbide precipitation at the grain boundaries. The ferrite dendrites being the first to solidify had a lathy morphology and partly transforms into austenite after solidification by diffusion controlled mechanism.Figure 1
Fusion zone micrograph of E 312-16/10 welded joint.


### 3.1.2. Analysis of E 310-16/10 Micrograph

E 310-16/10 fusion zone micrograph is shown in Figure2. As can be seen from the micrograph, the primary austenite (white) formed directly from the liquid as a primary dendritic phase as well as a secondary phase around ferrite. The interdendritic ferrite (dark) had a vermicular morphology engulfed in the austenite matrix, with carbide precipitation along the grain boundaries.Figure 2
Fusion zone micrograph of E 310-16/10 welded joint.


### 3.1.3. Analysis of E 308-16/12 (Lime-Titania) Micrograph

Fu et al. [12] noted that ferrite-austenite (FA) solidification duplex mode is characterized by the formation of primary ferrite plus three phase (ferrite, austenite, and liquid) reactions at the terminal solidification stage. The fusion zone micrograph of E 308-16/12 (lime-titania) joint shown in Figure 3 revealed a plenty of fine colonies of lathy ferrite (dark) embedded in austenite (white) matrix. The result was a duplex microstructure consisting of thin lathy ferrite and austenite.Figure 3
Fusion zone micrograph of E 308-16/12 (lime-titania) welded joint.


### 3.1.4. Analysis of TIG Micrograph

The fusion zone micrograph of TIG joint specimen shown in Figure4 revealed primary equiaxed dendritic and lathy ferrite (dark) enclosed in austenite (white) matrix, with the precipitation of carbides along grain boundaries.Figure 4
Fusion zone micrograph of TIG welded joint.


### 3.1.5. Analysis of E 308-16/12 (Rutile) Micrograph

The E 308-16/12 (rutile) weld joint micrograph is shown in Figure5. The figure revealed a duplex structure of ferrite and austenite. The primary ferrite (dark) dendrites having a combination of lathy and vermicular ferrite morphology contained in austenite (white) matrix and a precipitation of carbide along grain boundaries. The amount of retained ferrite in E 308-16/12 (rutile) weld metal was found to be less than TIG and E 308-16/12 (lime-titania) weld metals, respectively, but more than that observed in E 308-16/10 (rutile) weld metal.Figure 5
Fusion zone micrograph of E 308-16/12 (rutile) welded joint.


### 3.1.6. Analysis of E 308-16/10 (Rutile) Micrograph

The fusion zone micrograph of the E 308-16/10 (rutile) joint shown in Figure6 revealed a duplex structure consisting of ferrite (dark) and austenite (white). The primary ferrite had a thin lathy morphology engulfed by austenite which grew epitaxially and fills the interdendritic region of the primary ferrite. Carbide precipitation was also observed along the grain boundaries.Figure 6
Fusion zone micrograph of E 308-16/10 (rutile) welded joint.


## 3.1.1. Analysis of E 312-16/10 Micrograph

The micrograph of E 312-16/10 fusion zone test specimen shown in Figure1 revealed a primary ferrite (dark) matrix containing secondary austenite (white) and carbide precipitation at the grain boundaries. The ferrite dendrites being the first to solidify had a lathy morphology and partly transforms into austenite after solidification by diffusion controlled mechanism.Figure 1
Fusion zone micrograph of E 312-16/10 welded joint.


## 3.1.2. Analysis of E 310-16/10 Micrograph

E 310-16/10 fusion zone micrograph is shown in Figure2. As can be seen from the micrograph, the primary austenite (white) formed directly from the liquid as a primary dendritic phase as well as a secondary phase around ferrite. The interdendritic ferrite (dark) had a vermicular morphology engulfed in the austenite matrix, with carbide precipitation along the grain boundaries.Figure 2
Fusion zone micrograph of E 310-16/10 welded joint.


## 3.1.3. Analysis of E 308-16/12 (Lime-Titania) Micrograph

Fu et al. [12] noted that ferrite-austenite (FA) solidification duplex mode is characterized by the formation of primary ferrite plus three phase (ferrite, austenite, and liquid) reactions at the terminal solidification stage. The fusion zone micrograph of E 308-16/12 (lime-titania) joint shown in Figure 3 revealed a plenty of fine colonies of lathy ferrite (dark) embedded in austenite (white) matrix. The result was a duplex microstructure consisting of thin lathy ferrite and austenite.Figure 3
Fusion zone micrograph of E 308-16/12 (lime-titania) welded joint.


## 3.1.4. Analysis of TIG Micrograph

The fusion zone micrograph of TIG joint specimen shown in Figure4 revealed primary equiaxed dendritic and lathy ferrite (dark) enclosed in austenite (white) matrix, with the precipitation of carbides along grain boundaries.Figure 4
Fusion zone micrograph of TIG welded joint.


## 3.1.5. Analysis of E 308-16/12 (Rutile) Micrograph

The E 308-16/12 (rutile) weld joint micrograph is shown in Figure5. The figure revealed a duplex structure of ferrite and austenite. The primary ferrite (dark) dendrites having a combination of lathy and vermicular ferrite morphology contained in austenite (white) matrix and a precipitation of carbide along grain boundaries. The amount of retained ferrite in E 308-16/12 (rutile) weld metal was found to be less than TIG and E 308-16/12 (lime-titania) weld metals, respectively, but more than that observed in E 308-16/10 (rutile) weld metal.Figure 5
Fusion zone micrograph of E 308-16/12 (rutile) welded joint.


## 3.1.6. Analysis of E 308-16/10 (Rutile) Micrograph

The fusion zone micrograph of the E 308-16/10 (rutile) joint shown in Figure6 revealed a duplex structure consisting of ferrite (dark) and austenite (white). The primary ferrite had a thin lathy morphology engulfed by austenite which grew epitaxially and fills the interdendritic region of the primary ferrite. Carbide precipitation was also observed along the grain boundaries.Figure 6
Fusion zone micrograph of E 308-16/10 (rutile) welded joint.


## 3.2. Effect of Electrode Types on the Solidification Mode of Austenitic Stainless Steel Weld Metal

The results displayed in Table4 showed that the type of electrode selected in the welding of 304H stainless steel component affects the solidification microstructure of the weld metal. It was found that the TIG autogenous weld (Figure 4) had nearly the same solidification microstructure (FA) with the parent material (Figure 7), a result which was highly anticipated since there was no filler dilution in the completed weld as the tungsten electrode was nonconsumable. Weldments produced from E 308-16/12 (rutile), E 308-16/10 (rutile), and E 308-16/12 (lime-titania) electrodes had a duplex structure of ferrite-austenite (FA) with more or less amount of retained ferrite. Filler rod or electrode dilution is believed to be responsible for the evolved microstructure and solidification mode as shown in the results of the fusion zones micrographs of the E 308-16/12 (lime-titania), E 308-16/12 (rutile), and E 308-16/10 (rutile) joints displayed in Figures 3, 5, and 6, respectively. Joints produced from E 310-16/10 electrode (Figure 2) had austenite solidification mode whereas the joints made from E 312-16/10 (Figure 1) solidified with a primary ferrite solidification mode. The compromise reached between the parent material composition and filler rod or electrode dilution was found to be the major factor which determined the weld metal final microstructure and solidification mode. The findings of this research were found to be in line with the results of many researchers [5, 6, 12–15].Table 4
Values of Creq., Nieq., Creq./Nieq. ratio, and (P + S) wt.% of the tested weld joints.
Weld joints
Cr
eq.
Ni
eq.
Creq./Nieq.
(P + S) wt.%
Ferrite number (FN)
Solidification mode
E 308-16/12(rutile)weld joint
17.3019
9.7480
1.7750
0.0171
6
Ferrite-austenite (FA)
E 308-16/10(rutile)weld joint
17.2042
9.8678
1.7435
0.0094
5-6
Ferrite-austenite (FA)
E 308-16/12 (lime-titania) joint
19.8223
11.3915
1.7401
0.0086
10
Ferrite-austenite (FA)
E 310-16/10 weld joint
24.0273
22.7530
1.0560
0.0150
0-1
Austenite (A)
E 312-16/10 weld joint
26.8069
12.9698
2.0669
0.0140
50–55
Ferrite (F)
TIG weld joint
18.6387
10.9375
1.7041
0.0068Figure 7
Micrograph of the unwelded parent material.


## 3.3. Effect of Electrode Types on Weld Metal Composition and Cracking Propensity

The results of chemical analysis (presented in Table5) carried out on the weldments showed that electrode types have effect on the weld metal composition. The TIG autogenous weldment had nearly the same composition and Chromium-Nickel equivalence as that of the unwelded parent metal. However, remarkable difference in weld metal constitution was observed in the joints produced from the various electrodes relative to the Chromium-Nickel equivalence of the parent material. The Chromium-Nickel equivalence results, calculated for each weld joints and presented in Table 4, were obtained by using the the 1992 Welding Research Council model equation culled from Kotecki and Siewert [16]:(1)Creq.=Cr+Mo+0.7NbNieq.=Ni+35C+20N+0.25Cu,where, Creq. = Chromium equivalent and Nieq. = Nickel equivalent.Table 5
Chemical composition of the weld joints.
Elements wt.%
E 308-16/12 (rutile) weld
E 308-16/10 (rutile) weld
E 308-16/12 (lime-titania) weld
E 310-16/10 weld
E 312-16/10 weld
TIG weld
Carbon, C
0.0710
0.0730
0.0740
0.1350
0.0920
0.0600
Silicon, S
0.6900
0.6300
0.4900
0.5100
0.9100
0.3760
Manganese, Mn
1.2200
1.1800
1.3900
1.8700
1.3200
1.6200
Phosphorus, P
0.0061
0.0010
0.0010
0.0010
0.0010
0.0022
Sulphur, S
0.0110
0.0084
0.0076
0.0140
0.0130
0.0046
Chromium, Cr
17.1500
17.0200
19.5700
23.8500
26.7100
18.4500
Nickel, Ni
7.1900
7.2100
8.7400
17.9900
9.7300
8.7900
Molybdenum, Mo
0.1330
0.1660
0.2320
0.1570
0.0640
0.1740
Aluminium, Al
0.0055
0.0049
0.0056
0.0170
0.0072
0.0055
Copper, Cu
0.2920
0.4110
0.2460
0.1520
0.0790
0.1900
Cobalt, Co
0.0830
0.0960
0.1120
0.0770
0.0640
0.1170
Titanium, Ti
0.0240
0.0190
0.0110
0.4250
0.0160
0.0010
Niobium, Nb
0.0270
0.0260
0.0290
0.0290
0.0470
0.0210
Vanadium, V
0.0680
0.0700
0.1050
0.1080
0.1190
0.0770
Tungsten, W
0.0100
0.0100
0.0100
0.0100
0.0100
0.0560
Lead, Pb
0.0034
0.0030
0.0030
0.0030
0.0030
0.0038
Boron, B
0.0021
0.0018
0.0016
0.0017
0.0012
0.0022
Tin, Sn
0.0100
0.0098
0.0090
0.0075
0.0110
0.0110
Arsenic, As
0.0860
0.0810
0.0930
0.0960
0.1160
0.0950
Bismuth, Bi
0.0015
0.0015
0.0015
0.0015
0.0015
0.0015
Calcium, Ca
0.0002
0.0002
0.0003
0.0024
0.0003
0.0003
Iron, Fe
72.9000
73.0000
68.9000
54.6000
60.7000
69.9000The results showed that solidification cracking of the weld joints was sensitive toCreq./Nieq. ratio and solidification mode of the welds. E 308-16/12 (lime-titania), TIG, E 308-16/12 (rutile), and E 308-16/10 (rutile) welds with primary ferrite-austenite solidification modes and 1.5<Creq./Nieq.<1.9 are immune to solidification cracking in the order of decreasing resistance to solidification cracking, respectively. E 312-16/10 weld with ferrite solidification mode and Creq./Nieq.>1.9 has low susceptibility to solidification cracking, whilst E 310-16/10 weld with primary austenite solidification mode, Creq./Nieq.<1.5, and (P + S) wt.% = 0.015 may be susceptible to solidification cracking. Filler rod or electrode dilution is one of the factors which determined the final weld metal composition and solidification mode. Since solidification cracking is sensitive to weld metal composition and solidification mode, it therefore follows that the type of electrode used during welding of ASS materials determines the weld metal solidification cracking propensity.These results were compared with the cracking susceptibility of 300 series stainless steel based on Cr-Ni equivalence according to Hammar and Svensson [17] and found to be consistent and also in line with the findings of Arantes and Trevisan [6], Baldev et al. [5], Korinko and Malene [18], and Brooks and Thompson [19] who affirmed that the propensity for solidification cracking in austenitic stainless steel is sensitive to the Creq./Nieq. ratio, (P + S) wt.%, and ferrite number of the weld metal and maintained that weld metal with solidified FA mode in the range of 1.5<Creq./Nieq.<1.9 is immune to solidification cracking, while those in the region of Creq./Nieq.>1.9 and Creq./Nieq.<1.5 have low resistance and susceptible to solidification cracking, respectively. Generally, it was found that (P + S) wt.% values were less than 0.02 in the final composition of the respective welded joints, which is below the critical level suggested by Arantes and Trevisan [6], necessary to induce cracking.The results also suggest that the type of electrode coating has effect on the weld metal properties. The electrodes used for the welding were designated “-16” which denotes rutile coating for stainless steel electrodes. Rutile coatings are titania-type based electrodes containing little proportion of other additives. However, E 308-16/12 (lime-titania) electrodes were coated with titanium calcium and contain lime which makes it distinct from the rutile category. The presence of lime (which is a slag former) in E 308-16/12 (lime-titania) electrode was relevant in slowing down the cooling rate of both the weld pool and the just solidified weld metal of the resultant weldment. This suggests the reason for the slight difference observed in properties (such as ductility and strain hardening exponent) of weldments produced from the E 308-16 (lime titania) with respect to E 308-16 (rutile) welding electrodes. Consequently, the weldment produced from E 308-16/12 (lime-titania) electrode has a higher ductility of about 36% (in terms of percentage elongation) compared to 26% and 18% obtained from weldments produced from E 308-16/10 (rutile) and E 308-16/12 (rutile) electrodes, respectively. This result is confirmed in the micrograph of E 308-16/12 (lime-titania) weldment which suggests that the ferrite dendrite had more time for growth in the region where delta ferrite is most stable (due to slower cooling rate offered by lime in the electrode coating) compared to the micrographs of E 308-16/10 (rutile) and E 308-16/12 (rutile) weldments.


## 4. Conclusion

The cracking of austenitic stainless steel (ASS) material during welding was successfully reviewed while investigating the microstructural propensity of an ASS component to solidification cracking. It was found that fabricated ASS components produced from E 308-16/12 (rutile), E 308-16/10 (rutile), E 308-16/12 (lime-titania) electrodes, and TIG joints (all having FA duplex mode of solidification and ratio of Cr to Ni equivalence in the range1.5<Creq./Nieq.<1.9) are resistant to solidification cracking. The E 308-16/12 (lime-titania) electrode (having ferrite number (FN) of 10) was observed to impact the highest resistance to cracking, followed by TIG joints (with FN of 8), E 308-16/12 (rutile) with FN = 6, and E 308-16/10 (rutile) with FN = 5.5 in that order. ASS components fabricated from E 312-16/10 electrode (produced a Creq./Nieq. ratio of about 2.01 which is greater than 1.9 and ferrite number of about 53% in the completed weld which is beyond 35% stipulated by Hull [8] and necessary to cause a shift from immunity zone to crack susceptible zone). They solidified with a ferrite mode and were found to show little resistance to solidification cracking. The E 310-16/10 electrode solidified with austenite mode and was found to be somewhat liable to solidification cracking since it produced a Creq./Nieq. ratio of about 1.01, which is less than 1.5 the value suggested by [6, 19–21] to prevent solidification cracking in the completed weld metal.



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*Source: 213258-2015-08-12.xml*