Tailoring a High Temperature Corrosion Resistant FeNiCrAl for Oxy-Combustion Application by Thermal Spray Coating and HIP

Abstract

Oxy-fuel combustion combined with CCS (carbon capture and storage) aims to decrease CO₂ emissions in energy production using fossil fuels. Oxygen firing changes power plant boiler conditions compared to conventional firing. Higher material temperatures and harsher and more variable environmental conditions cause new degradation processes that are inadequately understood at the moment. In this study, an Fe-Ni-Cr-Al alloy was developed based on thermodynamic simulations. The chosen composition was manufactured as powder by gas atomization. The powder was sieved into two fractions: The finer was used to produce thermal spray coatings by high velocity oxy-fuel (HVOF) and the coarser to manufacture bulk specimens by hot isostatic pressing (HIP). The high temperature corrosion properties of the manufactured FeNiCrAl coating and bulk material were tested in laboratory conditions simulating oxy-combustion. The manufacturing methods and the results of high temperature corrosion performance are presented. The corrosion performance of the coating was on average between the bulk steel references Sanicro 25 and TP347HFG.

1. Introduction

The energy sector is the largest CO₂ emitter globally [1]. One concept to reduce the CO₂ emissions originating from the use of fossil fuels in power generation is carbon capture and storage (CCS) [2,3]. Integrated oxy-combustion is considered as one of the most promising technologies to facilitate CO₂ capture, because it can be built as a retrofit solution for existing boilers [4]. The oxy-fuel process uses oxygen or oxygen-enriched air to reduce nitrogen in the flue gas and hence increase the CO₂ content to facilitate more efficient capture.

Oxy-fuel combustion can be expected to differ from combustion in air by modified distribution of fireside temperatures, much reduced NO_x emissions, increased levels of fireside CO₂ and H₂O with small amounts of O₂, Ar, N_2, and some impurities like SO₂ and Cl [5]. Due to recycling of flue gas in oxy-fired combustion compared to air firing, there is an increased risk of corrosive species enrichment in the flue gas environment [6,7]. These changes in the combustion gas chemistry will also affect the chemistry and formation of deposits. This may increase corrosion of the boiler components that are in contact with the combustion and flue gas environment [8,9,10]. Coatings are a promising approach to improve corrosion resistance because existing validated structural steels can be used as base material. Coatings can be tailored by composition and structure to give the best surface protection for selected conditions.

Several steels and alloys have been tested in air- and oxy-fuel combustion conditions [11,12,13,14,15]. These include low alloy steels (13CrMo44), ferritic steels (T91, T/P92), austenitic steels (1.4910, Super 304H, TP347HFG, 310N, Sanicro 25 and HR3C), and nickel base alloys (IN617 and IN740). Gagliano et al. [11] tested several candidate materials both in laboratory and field tests in advanced ultra-supercritical conditions. They discovered that a material’s resistance to coal ash corrosion is primarily dependent on the chromium content. Alloys containing chromium more than 22 wt % generally exhibited satisfactory corrosion resistance in laboratory tests. The field study showed that materials containing roughly 25 wt % chromium exhibited satisfactory resistance, regardless of the fireside corrosion mechanism. Hussain et al. [14] exposed nickel-based thermal spray coatings to corrosion testing simulating fireside corrosion in coal and biomass co-combustion at 650 °C. The best performing coating in the study was NiCr coating with 46 wt % of chromium.

In future power plants, oxy-combustion may cause serious corrosion problems to boiler components. Besides testing present available materials, development of new protective materials is essential. Iron-based high chromium content coatings with aluminium addition offer a promising and readily applied solution [16], but require further development and research. This paper presents the development of a new Fe-based alloy from thermodynamical calculations to laboratory testing under simulating oxy-combustion. The Fe-based alloy was tested as a coating manufactured by high velocity oxy-fuel (HVOF) thermal spray process and in a hot isostatic pressed (HIP) bulk form.

2. Experimental Section

The material tailoring for oxy-combustion conditions began with composition selection by thermodynamic calculation. Iron was chosen as the base material, because it is inexpensive, and cost effective material solutions are valued. The thermodynamic calculations were made with the FactSage 6.3 program using the FSsteel database and a custom-compiled database for the environment and deposit. Based on the calculations (Figure 1), Fe-30Ni-14.5Cr-3.5Al, the red dotted line in the Figure 1, was chosen as the material composition. The phase diagram (Figure 1) shows that at temperatures over 675 °C the structure should be fully austenitic (FCC_A1) with fully soluble alloying elements. The material might have some problems with the formation of a brittle σ-phase under temperature of 675 °C. Additionally Al₃Ni₆ precipitates can form under 675 °C.

Figure 1. Phase diagram of the designed FeNiCrAl alloy. Selected material composition is marked with a dotted line. FCC_A1 = austenitic and FCC_A2 = ferritic.

Figure 1. Phase diagram of the designed FeNiCrAl alloy. Selected material composition is marked with a dotted line. FCC_A1 = austenitic and FCC_A2 = ferritic.

Thermodynamic equilibrium calculations were made with a surplus amount of exposure gases (44% CO₂-30% H₂O-0.6% SO₂-0.2% HCl-N₂) and deposit (CaSO₄-0.55 wt % KCl). The results are shown in Figure 2, where it can be seen that at 650 °C, the equilibrium favors solid FeCr₂O₄ formation along with smaller amounts of FeO, FeS and FeAl₂O₄ on top of Fe and Ni, which have high stabilities according to the calculation. The salt and gas would react to form solid CaCO₃. Moving to 720 °C solid FeO is increasingly preferred while solid FeS is not. Solid CaAl₂O₄ should be formed instead of FeAl₂O₄ and solid CaS instead of CaCO₃.

Figure 2. Thermodynamic equilibrium of the selected test material in the test exposure atmosphere, and deposit as a function of temperature.

Figure 2. Thermodynamic equilibrium of the selected test material in the test exposure atmosphere, and deposit as a function of temperature.

Powder of the selected composition was prepared by a Hermiga 75/5VI high-pressure gas atomizer. The atomizer was a 5 kg batch atomizer with induction melting. Argon was used as atomization gas providing an oxygen level of below 1 ppm. The used atomization gas pressure was 5 MPa and the overpressure in the melt chamber was 0.025 MPa. The melting point of the alloy is around 1450 °C and the melt temperature was 1650 °C. The FeNiCrAl metal alloy was pre-alloyed to ensure homogenous composition. Chamber fraction of the atomized powder was sieved with 45 μm aperture. Undercut was used in thermal spraying and overcut (45–125 μm) in HIP. Cyclone fraction was not used as it was considered too fine.

Thermal spray with an HVOF torch was used for depositing coatings of the manufactured powder on X20CrMoV121 ferritic stainless steel cylinders with prior degreasing and grit blasting. In addition, nitrogen permeability test buttons and plates for cross sectioning were coated. The test buttons for nitrogen permeability are porous discs that allow gas to freely flow though, but dense enough to be coated without issues [17]. The used torch was DJ Hybrid (Diamond Jet Hybrid) and the -45 μm sieved chamber fraction was used as the powder. Table 1 presents the used spray parameters.

Table 1. Coating parameters for HVOF spray of the FeNiCrAl powder.

Torch	Nozzle	Stand Off	Air	Propane	O2	N2	Powder Feed
DJ	2701	230 mm	400 L/min	62.4 L/min	290 L/min	12.5 L/min	50 g/min

Table 1. Coating parameters for HVOF spray of the FeNiCrAl powder.

Torch	Nozzle	Stand Off	Air	Propane	O2	N2	Powder Feed
DJ	2701	230 mm	400 L/min	62.4 L/min	290 L/min	12.5 L/min	50 g/min

Hot isostatic pressing was performed using an Asea Mini Hipper QUINTUS Hot Isostatic Press type QIH-9. The overcut of the chamber fraction of the gas atomized powder was packed in an AISI 316L HIP capsule of Ø27/30 mm × 100 mm using mechanical pressing. The evacuation of the capsule was 24 h at room temperature down to a pressure level of 10⁻⁵ mbar. Used HIP parameters were 1150 °C/3 h/1000 bar.

High temperature corrosion testing in oxy-fuel combustion conditions was carried out at VTT in a laboratory scale under isothermal conditions at temperatures of 650 and 720 °C up to 1000 h using a furnace system schematically illustrated in Figure 3. The furnace consisted of a horizontal ceramic lined reaction tube and mass flow control systems to produce the targeted gas mixtures. The carrier gas mixture was passed through a humidifying unit containing deionized water before the furnace, to add moisture to the gas mixture. For preheating purposes the gas line goes through the length of the furnace tube before releasing the gas mixture at the other end. The used premixed gas composition was 44% CO₂-30% H₂O-0.6% SO₂-0.2% HCl-N₂. During the exposure the specimens were embedded on a CaSO₄-0.55 wt % KCl deposit. Due to space limitations, only one specimen of each type was exposed.

Figure 3. Schematic figure of the high temperature corrosion test system.

Figure 3. Schematic figure of the high temperature corrosion test system.

The coated specimen was in the shape of a cylinder with 15 mm diameter and 20 mm length and the surface was left as coated. The HIP’ed specimens were machined from 15 mm diameter bars to a disc shape with 15 mm diameter and 5 mm height and ground to 600 grit surface finish. Sanicro 25 (UNS S31035) and TP347HFG (UNS S34710) specimens with dimensions of 15 mm × 15 mm × 3 mm machined from thick walled tubes were used as reference specimens with the surfaces ground to 600 grit finish. Table 2 shows the chemical composition of the reference materials.

After the exposure in the simulated oxy-fuel combustion, metallographic cross-sections were prepared by cutting the samples, mounting them into resin and grinding and polishing with ethanol. Characterization was performed with an optical microscope and a FEI XL30 ESEM scanning electron microscope (SEM) equipped with a Thermo Fisher Scientific UltraDry energy dispersive X-ray detector (EDX). X-ray Diffraction (XRD) was performed on corrosion products of the coatings after exposure in the highest temperature. The aim of the materials performance assessment was to characterize the morphologies produced during the exposure testing and to determine the extent of metal damage caused to each specimen during the exposure.

Table 2. Chemical composition of bulk materials Sanicro 25 and TP347HFG by optical emission spectroscopy (OES).

Alloy	Cr	Ni	Mo	Nb	Fe	Other
TP347HFG	18.3	11.7	0.23	0.92	bal.	1.64 Mn, 0.33 Cu, 0.4 Si, 0.07 C
Sanicro 25	22.3	24.9	–	0.5	bal.	3.4 W, 1.5 Co, 2.9 Cu, 0.2 Si, 0.3 Mn, 0.24 N, 0.06C

Table 2. Chemical composition of bulk materials Sanicro 25 and TP347HFG by optical emission spectroscopy (OES).

Alloy	Cr	Ni	Mo	Nb	Fe	Other
TP347HFG	18.3	11.7	0.23	0.92	bal.	1.64 Mn, 0.33 Cu, 0.4 Si, 0.07 C
Sanicro 25	22.3	24.9	–	0.5	bal.	3.4 W, 1.5 Co, 2.9 Cu, 0.2 Si, 0.3 Mn, 0.24 N, 0.06C

3. Results

3.1. Powder Manufacturing and Consolidation

Particle sizes of the manufactured powder were measured using Malvern Mastersizer 3000. The -45 μm sieved powder had D10 15.1, D50 27.4 and D90 45.3 μm values and the 45–125 μm sieved powder had D10 34.7, D50 61.3 and D90 105 μm values. The coarser powder contained some fine particles below 45 μm although sieved with 45 μm sieve. This was because of clogging of the sieve and perhaps too short a sieving time.

SEM images of the powders are presented in Figure 4 and Figure 5. They show some small satellite particles stuck on the surface of larger particles, but the amount of the satellites was so small that it was considered not to affect thermal spraying or HIP. Large magnification images (Figure 4b and Figure 5b) show grain structures. The grain structure is larger in large particles than in small particles due to faster cooling rate of the small particles. The grain structure cannot be detected on particles of less than 10 μm in diameter. EDX analysis of the composition of the powder is presented in Table 3.

An optical micrograph of the resulting microstructure of the HIP’ed alloy is presented in Figure 6. Coating microstructure on the cross-sectioning plate is shown in Figure 7. Coating thickness on the cylinders varied between 300 and 400 μm based on electromagnetic measurements (Elcometer). Porosity was measured by image analysis from several optical micrographs, and the porosity value was 0.31% in the coating and 1.61% in the HIP specimen. Nitrogen gas permeability was measured up to 7 bar using Kermetico GPT-02 testing rig and the results show that the coating was gas tight at the tested 270 μm thickness. This is in line with the low porosity value. The HIP specimen was not suitable to gas permeability testing, because it had too small diameter for the testing chamber. Coating hardness was tested with an instrumented indenter Zwick ZHU 0.2 using 0.3 kg load and performing six indents. The measured hardness was 361 HV0.3 with standard deviation of 40 HV0.3. Elastic modulus was calculated using the Oliver and Pharr method and the result was 160 MPa with standard deviation of 10 MPa. The considerable amount of standard deviation in the measurements is to be expected due to the varying microstructure. Table 4 summarizes the results.

Figure 4. SEM images of gas atomized FeNiCrAl powder sieved below 45 μm, magnifications with micron bars. (a) 100 μm; (b) 5 μm.

Figure 4. SEM images of gas atomized FeNiCrAl powder sieved below 45 μm, magnifications with micron bars. (a) 100 μm; (b) 5 μm.

Figure 5. SEM images of gas atomized FeNiCrAl powder sieved 45–125 μm, magnifications with micron bars. (a) 100 μm; (b) 5 μm.

Figure 5. SEM images of gas atomized FeNiCrAl powder sieved 45–125 μm, magnifications with micron bars. (a) 100 μm; (b) 5 μm.

Table 3. EDX analysis of the FeNiCrAl powder in wt % and calculated difference in %.

	Fe	Ni	Cr	Al
Target	Bal	30.0	14.5	3.5
EDX analysis	Bal	24.8	13.5	3.5
Difference (%)	–	−17.3	−6.9	0.0

Table 3. EDX analysis of the FeNiCrAl powder in wt % and calculated difference in %.

	Fe	Ni	Cr	Al
Target	Bal	30.0	14.5	3.5
EDX analysis	Bal	24.8	13.5	3.5
Difference (%)	–	−17.3	−6.9	0.0

Figure 6. Microstructure of the HIP’ed FeNiCrAl alloy before testing.

Figure 6. Microstructure of the HIP’ed FeNiCrAl alloy before testing.

Figure 7. Optical micrograph of a cross-section of HVOF DJ Hybrid sprayed FeNiCrAl coating before testing.

Figure 7. Optical micrograph of a cross-section of HVOF DJ Hybrid sprayed FeNiCrAl coating before testing.

Table 4. Indentation results for the HVOF thermal spray coating.

Coating Method	Hardness (HV0.3)	STDEV	E (Mpa)	STDEV	n
DJ Hybrid	361	40	160	10	6

Table 4. Indentation results for the HVOF thermal spray coating.

Coating Method	Hardness (HV0.3)	STDEV	E (Mpa)	STDEV	n
DJ Hybrid	361	40	160	10	6

3.2. Exposure at 650 °C

The DJ Hybrid sprayed FeCrNiAl coating had protected the X20 stainless steel substrate material during the 700 h exposure at 650 °C (Figure 8). Thick salt deposits had stuck on the coated specimen. Average outer corrosion product thickness on the deposit side was measured from the cross section to be 60 μm. The measurements were complicated by some corrosion products that had diffused into the deposits. In addition, there was 20 μm of internal corrosion in the coating.

Bulk reference materials were exposed for 1000 h. During the exposure, TP347HFG steel had formed a 100 μm thick corrosion product layer plus 30 μm of internal corrosion through grain boundaries. Sanicro 25 steel had formed a 200 to 500 μm thick corrosion layer and 20 to 50 μm of internal corrosion through grain boundaries. EDX analysis revealed sulfur in the grain boundaries. Table 5 summarizes all the corrosion layer thicknesses at 650 °C.

Figure 8. SEM image of the HVOF DJ Hybrid sprayed FeNiCrAl coating cross-section after the exposure at 650 °C for 700 h.

Figure 8. SEM image of the HVOF DJ Hybrid sprayed FeNiCrAl coating cross-section after the exposure at 650 °C for 700 h.

Table 5. Corrosion layer thicknesses in μm at 650 °C. HIP sample was not exposed at this temperature. The HVOF coating was exposed for 700 h while the others were exposed for 1000 h.

Layer	HVOF (DJ)	TP347HFG	Sanicro 25
Outer layer(s)	60	100	200–500
Internal	20	30	20–50

Table 5. Corrosion layer thicknesses in μm at 650 °C. HIP sample was not exposed at this temperature. The HVOF coating was exposed for 700 h while the others were exposed for 1000 h.

Layer	HVOF (DJ)	TP347HFG	Sanicro 25
Outer layer(s)	60	100	200–500
Internal	20	30	20–50

3.3. Exposure at 720 °C

At 720 °C, an average corrosion product layer thickness of 240 μm was measured for the DJ Hybrid sprayed coating. However, there was sulfur penetration through the coating all the way to the substrate, 250 μm below the remaining coating surface (Figure 9). Figure 9b shows that the sulfur content is highest at the corrosion front and approximately 100 μm inwards to the coating. Cr and O can be found above the corrosion front as a thick and porous layer. Below the layer the coating depleted of Cr, although there is some left. XRD analysis performed on the corrosion products of the coating revealed Fe₂O₃, FeS₂, FeCr₂O₄.

Figure 9. (a) SEM image of a cross-section of the HVOF DJ sprayed FeNiCrAl coating after the exposure at 720 °C for 700 h; (b) EDS elemental maps of the area shown in (a).

Figure 9. (a) SEM image of a cross-section of the HVOF DJ sprayed FeNiCrAl coating after the exposure at 720 °C for 700 h; (b) EDS elemental maps of the area shown in (a).

HIP’ed specimen exposed at 720 °C for 1000 h had corrosion products partially spalled off. There was from 30 to 50 μm of continuous corrosion layer left on the surface and internal corrosion from 50 μm up to a depth of 170 μm (Figure 10). The internal corrosion had first progressed through particle boundaries, some of which had clear gaps, and then through grain boundaries inside the particles (Figure 11a). EDX map (Figure 11b) shows that Cr was removed from particle boundaries where the corrosion progressed. Al was enriched at the particle boundaries and on top of the area where individual particles can still be distinguished. A Cr-rich layer was formed above the Al-rich layer.

Figure 10. SEM image of HIP (FeNiCrAl) cross-section.

Figure 10. SEM image of HIP (FeNiCrAl) cross-section.

Figure 11. (a) SEM image of HIP (FeNiCrAl) cross-section near the surface after the exposure at 720 °C for 700 h; (b) EDX elemental map of the same area.

Figure 11. (a) SEM image of HIP (FeNiCrAl) cross-section near the surface after the exposure at 720 °C for 700 h; (b) EDX elemental map of the same area.

The bulk reference material TP347HFG had corrosion layer thickness of 100 μm on the surface after the 1000 h exposure at 720 °C (Figure 12). However, the outer layer of the oxide was detached. In addition, there was up to 100 μm of internal degradation. EDX analyses showed sulfur penetration through grain boundaries. Small and isolated Ni and Nb rich areas can still be observed within the oxide layer along with S at matching locations. Sanicro 25 (Figure 13) had 300 μm of corrosion products on the surface. However, some spallation had also occurred in this case. Internal corrosion for Sanicro 25 ranged from 300 to 500 μm. The corrosion front appears to be depleted of Cr, while Ni is enriched (Figure 13b). S and Cl traces were found at grain boundaries, which were the main route for corrosion. Table 6 summarizes all the corrosion layer thicknesses at 720 °C.

Figure 12. (a) SEM image of TP347HFG steel cross-section near the surface after the exposure at 720 °C for 1000 h; (b) EDX elemental map of the corrosion front at a higher magnification.

Figure 12. (a) SEM image of TP347HFG steel cross-section near the surface after the exposure at 720 °C for 1000 h; (b) EDX elemental map of the corrosion front at a higher magnification.

Figure 13. (a) SEM image of Sanicro 25 steel cross-section near the surface after the exposure at 720 °C for 1000 h; (b) EDX elemental map of the same area.

Figure 13. (a) SEM image of Sanicro 25 steel cross-section near the surface after the exposure at 720 °C for 1000 h; (b) EDX elemental map of the same area.

Table 6. Corrosion layer thicknesses in μm at 720 °C. Some of the external corrosion layers had spalled off, indicated by the “+” signs. The HVOF coating was exposed for 700 h while the others were exposed for 1000 h.

Layer	HVOF (DJ)	HIP	TP347HFG	Sanicro 25
Outer layer(s)	240	50+	100+	300+
Internal	250	50–170	100	300–500

Table 6. Corrosion layer thicknesses in μm at 720 °C. Some of the external corrosion layers had spalled off, indicated by the “+” signs. The HVOF coating was exposed for 700 h while the others were exposed for 1000 h.

Layer	HVOF (DJ)	HIP	TP347HFG	Sanicro 25
Outer layer(s)	240	50+	100+	300+
Internal	250	50–170	100	300–500

4. Discussion

As expected, the results showed that a higher temperature yielded higher amounts of corrosion. The corrosion mechanism appeared to be the same in both temperatures: sulfidation, possibly preceded by chlorine corrosion. The formation of such types of corrosion products cause by chlorine corrosion have also been reported by Oksa et al. [17]. Alkali chlorides in deposits may cause accelerated corrosion well below the melting point of KCl [18]. Gases containing HCl for example, can influence the corrosion caused by other mechanisms, such as sulfidation, by breaking down the protective oxides and allowing corrosive species to reach the metal surface [18]. Similar results have been reported by Haanappel et al. [19], who found that HCl in an oxidizing-sulfidizing environment increased the corrosion rate significantly and made the scales thick, porous and non-protective, comparable to the results of this study.

The manufactured FeNiCrAl composition was both thermal sprayed and HIP’ed so that the effect of microstructure to the performance could be seen. The structure of the DJ Hybrid coating showed some large splats, which were nicely deformed, and some completely oxidized small particles. The coating could have been improved by using a tighter powder fraction, either by removing the smallest particles and using current spray parameters, or by removing the largest particles and using cooler spray parameters. The over-oxidized lamellae boundaries in the coating could have contained porosity or might have micro-cracked under thermal stress and therefore allow faster diffusion of corrosive species into the coating and enabled diffusion of coating element outward, as Ni and Fe were found diffused deep into the deposits. Having small lamellas lead to an increased amount of lamellae boundaries and hence higher diffusion when the boundaries act as diffusion paths. Aluminum did not effectively block the lamellae boundaries, and XRD results showed that the predicted phases did not form. This was likely due to the composition mismatch between the calculated and manufactured powder. Based on the EDX results of Table 3, there is room for optimization in the powder manufacturing, because the actual composition had 17% less Ni and 7% less Cr than planned. Al content was exactly as planned. Unfortunately, the HIP’ed specimen had large porosity between the particles, making it more difficult to compare with the other specimens as intended. However, the larger particles do show how the corrosive species diffused inside the particles through grain boundaries. The same was observed on a smaller scale in the coatings.

The exposure tests were conducted on single specimens, so the approach is guiding rather than statistical. TP347HFG performed well at 650 °C by having the second thinnest corrosion products (100 + 30 μm), being only slightly behind the HVOF coating, which would have had 86 + 29 μm if we assume linear growth from 700 h exposure to 1000 h. At 720 °C the oxide had spalled, but based on the amount of internal corrosion, the material could be the best performer of the experiment. The reference material Sanicro 25 had disastrous performance at both temperatures, even though it contained more Cr (22.5 vs. 18 wt %) and Ni (25 vs. 11 wt %) than the TP347HFG. Selective corrosion of Cr has been observed to increase in Cl containing atmospheres when Cr content increases [20]. However, the Cr difference of TP347HFG and Sanicro 25 is quite small compared to the performance difference. Therefore, the very poor performance of Sanicro 25 steel was more likely related to its Cu content.

When present in deposits, copper has been found to increase corrosion rates significantly in chlorine containing conditions by catalyzing the formation of elemental chlorine from HCl [21,22]. Because chemical composition of Sanicro 25 with higher Cr and Ni content would suggest that the material had better corrosion resistance than TP347HFG, we suggest that copper has probably had an influence on the high corrosion rate as an alloying element. Together with preferential removal of Cr at the corrosion front, copper may have reacted with chlorine and contributed to the very high corrosion rate of Sanicro 25. As a reference, TP347HFG and SAN25 have been tested in air- and oxy-firing conditions by Holcomb et al. [13]. The corrosion rates varied from 0–25 nm/h at 550 °C to 210–615 nm/h at corrosion peak temperature of about 700 °C, when chlorine was not present in the deposit.

5. Conclusions

This study presented material development from thermodynamic calculations of suitable composition to performance in a simulated oxy-fuel combustion environment. In between, there were steps for creating the desired composition in the form of a powder, and using two different consolidation methods to produce coating or bulk material from the powder. HVOF (DJ) coating had better performance than the reference materials at 650 °C. However, at 720 °C there was significant amount of sulfur penetration throughout the coating. The HIP’ed structure was hard to compare due to its porosity. Overall the best material in these experiments was the TP347HFG steel. In light of these results, the execution of the development chain has room for improvement and further research is required.