Microstructural behavior of SAF 2205 Duplex Stainless Steel Welded by Friction Hydro Pillar Processing

Abstract

The Friction Hydro-Pillar Process (FHPP) is an innovative process that has been recently studied regarding its possible in situ repair applications. There is still no literature about usage of the FHPP on duplex stainless steel (DSS) base materials to smaller forces than 25 kN. The investigation on DSS processing is crucial due his wide variety of critical uses in pipes and storage structures applied in chemical industry plants, where usual welding processes may lead to safety concerns. The aim of this study is to qualify the processing of SAF 2205 (UNS 31803) duplex stainless steel welded joints using FHPP as feasible repair procedure. For this, the studied samples were welded applying a range of axial forces. The welded joints were characterized by, α/γ phase ratio, intermetallic quantification, austenite spacing measurement, microhardness profile and microstructural qualitative studies. The results showed the efficiency in repair of the FHPP process on the production of DSS joints according with the material recommendations from the standard DNV-RP-F112.

Keywords
Friction Hydro Pillar Processing; Duplex stainless steel; Repair; Microstructure

1. Introduction

The duplex stainless steels (DSSs), characterized by ferrite-austenite dual phase microstructures, are widely used in petrochemical, oil, chemical, nuclear and marine industries because of their combination of high mechanical strength and good corrosion resistance in aggressive environments¹. The SAF 2205 may be referred as the most extensively DSS used nowadays, constituting approximately 80% of its total amount consumed². However, due to high chromium (~22%Cr) and molybdenum (~3%Mo) contents and their high diffusion rate in ferrite, DSSs present a tendency to form unwanted secondary phases during exposure to temperatures between 400 and 1000 ºC^3,4. Besides, thermal processes that involve long exposition periods of DSS to high temperature, may aggravate the appearance of Mo-enriched χ phase^3,5. The high degree of χ phase precipitation is also associated to negative effects on corrosion and mechanical properties^6,7.

In industrial plants it is common to have the requirement of maintenance intervention due to safety regulation. Normally, conventional arc welding processes are employed in cases where structure repairs are needed. The concept of filling weld repair of localized damage process which allow fast, efficient and cost-effective led to the design of Friction Hydro Pillar Processing (FHPP)^6,8-10macrostructure and mechanical properties in AISI 4140 steel. It also presents 3D residual stress data for a typical friction taper stud weld. Applied downwards force, rotational speed and plunge depth (equivalent to consumable length. The FHPP was initially developed by specialists at TWI (The Welding Institute) aiming to create a safer and more efficient technique weld joints production and localized damage repairing in metallic structures¹¹. The process involves firstly the machining a hole in order to remove the region containing a previous detrimental discontinuity followed by co-axial rotation a consumable plug under controlled load generating frictional heat which continuously produces a plasticized layer responsible for the complete hole filling^8,12 (Figure 1 and Figure 2). This process occur in the materials in solid state, promoting then less microstructural alteration and lower residual stress levels than conventional arc welding, which depends upon the materials fusion and solidification. Hence, the result of having minor microestructural modifications in base materials is the possibility of using this welding process in situ, i.e., without the necessity of any requirement of plant shutdown in order to repair a single or group of components. Consequently, FHPP welds may offer considerable time, energy and cost savings over fusion welding in repairs applications¹⁰ macrostructure and mechanical properties in AISI 4140 steel. It also presents 3D residual stress data for a typical friction taper stud weld. Applied downwards force, rotational speed and plunge depth (equivalent to consumable length. Further research on the FHPP technique extended its potential applications to crack repair^11,13, hole filling^9,14, cladding and material processing⁸. Due to this processing adaptable quality, further works showed its applicability in different materials such as low carbon steels with different axial forces, 50, 200, 250, 300, 350 and 400 kN^8,9,15,16. Pinheiro joined different magnesium (Mg) materials using FHPP¹⁷. This process was used on the repair of undersea structures, including oil pipelines^18-20. It was already studied FHPP process with DSS material, but the force was 200 kN which resulted joint with good toughness²¹. The FHPP can be automated⁶ and distance operated ensuring greater reproducibility¹⁹. This process may presents few disadvantages as lack of bond, incompletely filled groove and a complex mechanical and metallurgical characterization⁹.

Figure 1
Schematic illustration showing FHPP process. a) Rotating consumable plug co-axially, b) processing and pressed against structure.

Figure 2
FHPP Processing. a) Rotating consumable plug co-axially, b) processing and pressed against structure.

The aim of this study is to qualify the processing of SAF 2205 (UNS 31803) duplex stainless steel welded joints using FHPP as feasible repair procedure utilizing lower force than those used in last works. The motivation to this study is to generate knowledge about the FHPP process applied in SAF 2205 to be one more weld process capable to repairing localized damage in structures that use this type of material. The way to approach will be through metallurgical characterization and mechanical test.

2. Experimental procedure

As the base metal (BM) and the plug, the material selected was SAF 2205 (UNS 31803) duplex stainless steel. The chemical composition of those materials is shown in Table 1. Before welding, DSS 2205 base metal were machined into four specimens in the dimensions of 40 mm x 40 mm x 12 mm (length x width x thickness). For each specimen, a blind hole of 8.6 mm depth and 20º taper angle were drilled at the center of the samples. Furthermore, four DSS 2205 studs were lathed into consumable plugs of 15º tapered head. The hole and the plug design are shown in Figure 3.

Table 1
Chemical composition of base material (BM) and Plug (wt%).

Material	C	Si	Mn	P	S	Cr	Mo	Ni	Co	Cu	Nb	Ti	V	W	N	Balance
BM	0,02	0,52	1,65	0,02	0,003	22,9	3,16	4,74	0,05	0,19	0,03	0,004	0,08	0,09	0,19	Fe
Plug	0,03	0,57	1,45	0,02	0,003	23	2,72	5,09	0,04	0,08	0,03	0,004	0,07	0,09	0,2	Fe

Figure 3
Dimensions of tapered consumable plugs and tapered hole.

An appropriate friction hydro pillar process system was used for carrying out the welding experiment. The welding system is composed by a hydraulic power system to applying force (kN), a high rotational speed welding head (rpm), an automatic control system, a data monitor and an acquisition data system. The welding system can reach 8000 rpm and 25 kN axially pressure force from a hydro-cylinder. In this welding process, the main settings are rotational speed, axial force, burn-off, and forging force.

To determine the welding parameters, studies cited previously were taken in consideration. The samples were divided according the welding and same forging force applied, which varied between 5 and 25 kN. For the process of the samples, the welding parameters were tested and determined according Table 2.

Table 2
Welding parameters.

Sample	Rotational speed [rpm]	Welding force [kN]	Forging force [kN]	Burn- off [mm]	Forging time [s]
5 kN	5000	5	5	6	10
10 kN	5000	10	10	6	10
18 kN	7000	18	18	9	10
25 kN	7000	25	25	9	10

For the microstructural study and microhardness test, the as-welded parts were cut into samples. The position of microstructural study was in the mixing zone of the joint weld. The cross-sections of the samples were etched with Behara modified reagent, which consist in a mixture of 20 mL hydrochloric acid, 80 mL deionized water, 1 g K₂S₂O₅ and 2 g NH₄HF₂. The samples were etched during 15 s to 2 min by immersion. To the microstructural analysis, phase ratio α/γ and γ spacing were used an OLYMPUS BX51M optical microscope (OM) and a SHIMADSU SSX-550 scanning electron microscope (SEM) with EDX to intermetallic analysis. Microhardness studies were carried out on the different weldments regions formed during the process using an INSTRON Tukon 2100-B Vicker's micro-hardness tester. A standard load of 500 gf was applied for a dwell period of 10 s and the measurements were carried out at regular intervals of 0.25 mm in three different intervals of 2 mm from the upper surface of the welded joint.

3. Results and Discussion

In the FHPP process, the axial force is linked to the heat input during the welding to ensure an appropriate bond. The rotational speed is important to mixture the material of base metal with the plug in the mixing zone to ensure a joint without defects. These factors associated with the burn off determine the welding time. The acquisition data in different welding conditions were then organized and compared (Figure 4). The recorded parameters were rotational speed, time, axial force, and axial displacement.

Figure 4
Acquisition data in different welding conditions. a) Speed 5000 RPM, Burn-off 6 mm, Force 5 kN. b) Speed 5000 RPM, Burnoff 6 mm, Force 10 kN. c) Speed 7000 RPM, Burn-off 9 mm, Force 18 kN. d) Speed 7000 RPM, Burn-off 9 mm, Force 25 kN.

The deformation and the heat shortage occur frequently in earlier stages of the overall FHPP process, especially in the axial force increasing phase when the stable weld process has not yet been established. As the low heat input as the short thermoplastic flow and the plug plastic deformation during welding lead to defects. The first tests showed that smaller forces lead to soldering defects known as incomplete filling and lack of bond⁹. Considering the characteristic of FHPP, in a proper joint geometry design, the main reason for forming weld defects might be the insufficient frictional speed²². Welded joint micrographs of the plug lower curvature radius region of 5, 10, 18 and 25 kN cross-sections specimens are shown in Figure 5. Both the 5 kN (Figure 5-a) and the 10 kN (Figure 5-b) show incomplete filling while the 18 kN (Figure 5-c and Figure 6) shows adhesion but insufficient mixing. Lack of bond and incomplete filling are found in welds fabricated with relatively low rotational speed or low axial force. Lack of bond of the plug lower curvature radius region may appear due to inclusions and thermal contraction⁹.

Figure 5
Micrographs. a) The force 5 kN show incomplete. b) The force 10 kN show incomplete filling too. c) The force 18 kN show insufficient mixing. d) The force 25 kN show complete bonding.

Figure 6
Micrographs of 18 kN showing insufficient mixing and lack of bond.

3.1. 25 kN microstructures

The micrograph in Figure 5-d show that 25 kN welded joint with a complete bonding and therefore will be the only used in the following tests. To the 25 kN welded joint sample, the microstructural analysis showed different zones. These zones are normally called the Heat Affect Zone of Plug (HAZ-Plug), Thermo-Mechanically Affected Zone of Plug (TMAZ-Plug), Mixing Zone (MZ), Thermo-Mechanically Affected Zone of Base Material (TMAZ-BM) and heat Affected Zone of Base Material (HAZ-BM) respectively (Figure 7).

Figure 7
Schematic illustration showing the different zones observed.

Those DSS welded joint common microstructure zones are shown in Figure 8. In same Figure, to the next analysis, the microstructures were divided in regions called region A, region B, region C and region D. In the Mixing Zone, all three forms of austenite phase were observed (Figure 9), i.e. grain boundary allotriomorphs (GBA), Widmanstätten (WA) structure of austenite and transgranular austenite particles (IGA)²³. However WA was predominant and it occurs when higher heat input are provided²⁴. With coarsening of WA improving the low temperature toughness, affecting corrosion state²⁵.

Figure 8
Microstructure 25 kN zones divided into regions.

Figure 9
Mixing zone (MZ) shows Widmanstätten (WA), grain boundary allotriomorphs (GBA) and transgranular austenite particles (IGA).

The Figure 10-b-e-h show that the precipitation of secondary austenite in form of Widmanstätten needles from ferrite grain boundaries enhanced when deeper in the MZ. Yang et al²⁵ shown that both GBA and WA had higher chromium contents and PREN (Pitting Resistance Equivalent Number) values than IGA, indicating a better pitting resistance. Gunn²⁶ and Karlsson et al.²⁷ already had reached these results in their DSS studies. It was observed small amount of particles of transgranular austenite (IGA), because IGA requires more driving force to nucleate inside the grains²⁸. During cooling cycle, transformation of austenite phases was sufficient in MZ to satisfy the duplex criteria due to rapid cooling achieved which ensures mechanical properties. MZ gave ferrite levels of 55 to 68% that are according with the recommendations from the standard DNV-RP-F¹12. (Table 3), being important to mention that in different heights of MZ-Regions a gradual α-decrease was observed: A-MZ-68%, B-MZ-65%, C-MZ-61%, D-MZ-56%.

Figure 10
According to Figure 8 in different Heights, the a), d) and g) are TMAZ-Plug, the b), e) and h) are MZ, the c), f) and i) are TMAZ-BM. The j) k) and l) shows the detail of bonding tip plug.

Table 3
Ratio α/γ and γ spacing.

Region	Zone	α %	%RA α	γ%	%RA γ	γ spacing (μm)	%RA γ spacing
A	TMAZ-Plug	57,63	9,32	42,37	7,94	10,39	4,47
	MZ	67,69	12,51	32,31	4,34	22,78	6,96
	TMAZ-BM	61,17	5,75	38,83	5,96	14,76	3,34
	TMAZ-Plug	67,55	8,71	32,45	4,74	11,12	5,36
B	MZ	65,17	13,61	34,83	4,97	21,75	7,49
	TMAZ-BM	65,61	9,83	34,39	4,83	16,95	4,31
	TMAZ-Plug	64,70	7,25	35,3	5,12	18,83	5,82
C	MZ	61,09	11,54	38,91	6,07	19,26	7,38
	TMAZ-BM	66,43	9,89	33,57	4,64	17,70	6,49
	TMAZ-Plug	61,09	8,21	38,91	6,08	23,43	4,83
D	MZ	55,83	14,03	44,17	8,25	9,03	9,16
	TMAZ-BM	59,98	7,18	40,02	7,76	22,43	8,65
	Plug lengthwise	49,63	4,80	50,37	4,93	31,54	6,73
Non process material	Plug transverse	55,01	5,28	44,99	4,46	24,43	6,80
	BM	49,69	7,56	50,31	7,39	25,76	5,14

In the MZ, at the tip of the processed plug (Figure 10-l), is possible to see the formation of a microduplex structure. This microstructure results when a second phase precipitation precedes or occurs during recrystallization²⁹. This microduplex structure was classified with a super-plastic behavior (elongation of several 100% before failure)²⁶. According Gunn²⁶, this phenomenon requires slow strain rates (a few mm/min), temperature of at least 0.6 Tm (where Tm is the absolute melting temperature) and very fine structure. Some authors^4,26 describe ways to obtains this microduplex microstructure, but it was the first time cited in FHPP welds.

3.2. 25 kN phase ratio α/γ, γ spacing and χ-phase EDS analysis

Normally, all fabrication process that tends to decrease austenite spacing are favorable because decrease the free ferrite path which generally propagates Hydrogen Induced Stress Cracking (HISC). Offshore Standard DNV-RP-F112³⁰ confirm that materials with fine phase γ spacing have greater resistance to HISC than materials with coarse phase spacing. The austenite spacing is considered fine if it is less than 30 micrometers. In the next Table 3 is possible to see that the results as-welded of γ spacing and phase ratio α/γ are showing containing the %RA (relative accuracy) which proved satisfactory. Furthermore the Table 3 shows that the Austenite spacing in the MZ is approximately in the range of 4 to 24 µm with a gradual decreases when going from region A to D: A-MZ-23,88 µm, B-MZ-21,77 µm, C-MZ-16,74 µm, D-MZ-4,39 µm.

The weld metal and the HAZ in root area of the clad pipe seam welds, any pipe end clad welds and the seal welds of lined pipe shall be essentially free from grain boundary carbides, nitrides and intermetallic phases. Essentially free from intermetallic phases after processing implies that occasional strings of detrimental phases along the centerline of the base material is acceptable given that the phase content within one field of vision (at 400X magnification) is < 1.0% (max. 0.5% intermetallic phases)³¹. In the BM and MZ region, the intermetallic phases were not found. The analysis was taken in worst detected Region which was between the HAZ-plug and TMAZ-plug. The results at 400X magnification were < 0.42% intermetallic phases. In Figure 11 the microstructure of referred result. In that case, the intermetallic phase is the χ-phase according other researchers^7,32,33.

Figure 11
Microstructure of referred result used for measure % intermetallic phases according DNV-RP-F11230.

The intermetallic χ-phase (Figure 12) can be identified on the basis of BSE (back scattered electrons) contrast in SEM because chi phase is rich in the element molybdenum^7,34. Andrews³² and another researchers³³, showed that χ-phase appears only in the Fe-Cr-Mo ternary and in the Fe-Cr-Ni-Mo and Fe-Cr-Ni-Ti quaternary systems. The Energy-dispersive X-ray spectroscopy (EDS) showed that the large amount molybdenum in intermetallic phase Table 4.

Figure 12
Scanning electron microscopy micrographs of α, γ and χ phases of the duplex stainless steel Processed by FHPP. Etching: Behara modified.

Table 4
Contents of principal metallic elements in γ, α and χ-phases as determined by EDS after FHPP in DSS (wt.%).

	Si	Cr	Mn	Mo	Ni	Fe
γ	0.691	21.22	2.93	2.51	6.14	66.51
α	0.919	23.72	2.64	3.21	4.21	65.55
χ	0.716	23.74	1.44	11.84	2.26	55.26

3.3. 25 kN hardness analysis

During the processing, FHPP is produced by friction and pressure. In the final process has only the action of forging pressure which the consumable plug is pressed against base material causing a severe plastic deformation. It was proposed that three main strengthening mechanisms of weld zones for friction welding: strain hardening, decreasing grain size and microstructural transformation, and probably, are those strengthening mechanisms of FHPP welds. The hardness distribution profiles of 25 kN sample (Figure 13) which is evaluated according to the three lines testing. The results indicates that hardness values ranging from 250 HV0.5 to 290 HV0.5 are commonly found between MZ and TMAZ-Plug regions. Both in the zone HAZ-Plug as in zone HAZ-BM exhibit lower value in the range of 245-280 HV0.5, practically the same as BM. Besides, results along the four testing lines within MZ reveal that the hardness distribution is heterogeneous because has some singular points with higher hardness values. The increase of hardness between MZ and TMAZ-Plug indicates that materials in both regions are strengthened after welding. In previous works for FHPP^6,35 shows that hardness distribution difference around the zones is common. As shown in Figure 9 and Figure 10, the microstructure of MZ is mainly secondary austenite in the form of Widmanstätten needles from the ferrite grain boundaries.

Figure 13
Hardness distribution in 25 kN sample.

4 Conclusions

For the first time this DSS material was investigated in FHPP welds with forces variation from 5 to 25 kN. The results showed the efficiency in DSS structure repair using FHPP with the 25 kN force. It was possible the production of DSS joints according with the recommendations from the standard DNV-RP-F112. The following conclusions could be drawn:

The tests showed that smaller forces lead to soldering defects known as incomplete filling and lack of bond. The FHPP with force of 25 kN was approved according the standard requirements as welded joint because was the only with a complete mixing and bonding without defects.

In Mixing zone (MZ) at the tip of the processed plug was possible to see a microduplex structure formed. It was the first time in which the microduplex structure was cited with the FHPP process and the DSS material.

In this investigation, microstructure of FHPP process in DSS reveals three distinct forms of austenite phases i.e. grain boundary allotriomorphs (GBA), Widmanstätten structure (WA) and transgranular austenite particles (IGA). The microstructure of the weldment shows excessive formation of secondary austenite phases in the form of Widmanstätten structure in the Mix zone (MZ) of the weld. The precipitation of Widmanstätten needles from the ferrite grain boundaries increases the strenght in this region.

The results as-welded γ spacing and α levels was approved according the Offshore Standard DNV-RP-F112 requirements.

The intermetallic χ-phase was identified. All Regions was analyzed and the one with the higher amount of χ-phase presented was between the HAZ-plug and TMAZ-plug. However the results were < 0.42% intermetallic phases which is satisfactory according the standard requirements DNV AS.

Occurred a low variation of the microhardness. The increase of hardness between MZ and TMAZ-Plug indicates that materials in both regions are strengthened after FHPP process.

5.ACKNOWLEDGMENTS

The authors acknowledge the financial support of LAMEF and especially Diogo Busati, Francisco Bandeira, Facundo Lopez and Rafael Eugênio for supporting the experiment and positive suggestions.

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Publication Dates

• Publication in this collection
  18 July 2016
• Date of issue
  Jul-Aug 2016

History

• Received
  14 Jan 2016
• Reviewed
  07 May 2016
• Accepted
  24 June 2016