Page 1
A Thesis
Entitled
Evaluation of Lanthanum Phosphate Ceramic as Alternative Nozzle Material in Sulfuric
Acid Incineration
By
Jesse C. Wright
Submitted as partial fulfillment of the requirements for
The Master of Science in
Chemical Engineering
Advisor: Dr. Abdul-Majeed Azad
College of Graduate Studies
The University of Toledo
May 2008
Page 2
The University of Toledo
College of Engineering
I HEREBY RECOMMEND THAT THE THESIS PREPARED UNDER MY
SUPERVISION BY Jesse C. Wright
ENTITLED Evaluation of Lanthanum Phosphate Ceramic as Alternative Nozzle
Material in Sulfuric Acid Incineration
BE ACCEPTED IN PARTIAL FULFILLMENT OF THE REQUIREMENTS FOR THE
DEGREE OF MASTER OF SCIENCE IN CHEMICAL ENGINEERING
Thesis Advisor: Dr. Abdul-Majeed Azad
Recommendation Concurred by
Dr. John P. Dismukes
Committee
on
Dr. Michael R. Cameron Final Examination
Dean, College of Engineering
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iii
An Abstract of
Evaluation of Lanthanum Phosphate Ceramic as Alternative Nozzle Material in Sulfuric
Acid Incineration
Jesse C Wright
Submitted as partial fulfillment of the requirements for
The Master of Chemical Engineering
The University of Toledo
May 2008
Sulfuric acid is one of the largest produced chemicals in the world and a large
percentage is recycled through thermal decomposition. The nozzles that inject spent
sulfuric acid into a thermal decomposition furnace plague the process with high levels of
corrosion. The interface of high temperature gas and aqueous sulfuric acid creates a
unique mode of corrosion. A search for a nozzle material that is resistant to such rapid
deterioration and expensive replacement is therefore warranted. Ceramics being
somewhat superior to metals and alloys in terms of their corrosion resistance in an acidic
medium, lanthanum phosphate monazite was considered as a new alternative material to
compose the nozzles and thus increase the resistance to corrosive failure.
Lanthanum phosphate monazite was selected for this purpose because of its wide
range of applications in extreme and corrosive atmospheres. The material has been
reported to perform well as a ceramic for radioactive waste storage, ceramic matrix
composites in turbine applications, a machinable ceramic, and a good proton conductor
for sensors and fuel cells. Lanthanum phosphate monazite was thought to be a good
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candidate to compose the nozzles because of the similarities with its other applications
under conditions that a nozzle in spent acid treatment typically experiences. Testing was
done to determine if the material could function as a structural ceramic substitute to the
currently used alloys, at the operating temperatures and, if it would withstand the aqueous
mode of corrosion and the high temperature gaseous corrosion. During the material
corrosion analysis details of the corrosion process within the furnace were further
defined. The results were compared to other materials for analysis and recommendation.
The findings establish a clear set of directives for future research considering nozzle
corrosion, including the promising potential of using Al2O3-LaPO4 composite as the new
material.
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Acknowledgements
I would like to thank my adviser, Dr. Abdul-Majeed Azad, for his support and
assistance. My circumstances of work and school required much patience and
understanding. Also, a special thanks to Sathees Kesavan and Desikan Sundararajan,
each generously donated their expertise and time to help me conduct my research.
I would also like to thank Jim Rapp and Neil Nofziger for sharing their research
and information that assisted me in determining the direction of my research. I would
also like to thank Chris Caspers of Federal Mogul. The equipment in his laboratory was
instrumental in defining the physical properties of the materials being studied. Chris
kindly assisted me in running many tests and procedures.
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Table of Contents
ABSTRACT.....................................................................................................................III
ACKNOWLEDGEMENTS ............................................................................................ V
TABLE OF CONTENTS ...............................................................................................VI
LIST OF TABLES .......................................................................................................... IX
LIST OF FIGURES ......................................................................................................... X
INTRODUCTION............................................................................................................. 1
1.1 SULFURIC ACID REGENERATION PROCESS ..................................................................... 1
1.2 INJECTION NOZZLES ....................................................................................................... 2
1.3 MOTIVATION.................................................................................................................. 4
1.4 RESEARCH FOCUS ......................................................................................................... 5
LITERATURE REVIEW ................................................................................................ 6
2.1 LANTHANUM PHOSPHATE MONAZITE ............................................................................ 6
2.1.1 COMBUSTION APPLICATIONS 6
2.1.2 MACHINABILITY CHARACTERISTICS 8
2.1.3 PHYSICAL PROPERTIES 10
2.1.4 STOICHIOMETRY 12
2.2 MICROWAVE SINTERING .............................................................................................. 15
EXPERIMENTAL.......................................................................................................... 17
3.1 EXPERIMENTAL ............................................................................................................ 17
3.1.1 PROCESS CONDITIONS 17
3.1.2 BOILING ACID 20
3.2 SYNTHESIS OF LAPO4 .................................................................................................. 21
3.2.1 POWDER SYNTHESIS 21
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3.2.2 SINTERING 25
3.3 CORROSION TEST ......................................................................................................... 26
3.3.1 BOILING ACID EXPERIMENT 26
3.3.1 ACID SAMPLES 28
RESULTS AND DISCUSSION ..................................................................................... 29
4.1 MATERIAL PROPERTIES OF LANTHANUM PHOSPHATE, LAPO4 .................................... 29
4.1.1 COEFFICIENT OF THERMAL EXPANSION 29
4.1.2 THERMAL AND THERMOGRAVIMETRIC ANALYSIS 31
4.1.3 MACHINABILITY 34
4.2 CORROSION TESTS ....................................................................................................... 35
4.2.1 FIELD TEST 35
4.2.2 CONSISTENCY OF BOILING ACID TEST PROCEDURE 37
4.2.3 HASTELLOY C22 BOIL TESTS 39
4.2.4 AL2O3 BOILING ACID TESTS 40
4.2.5 LAPO4 BOILING ACID TESTS 41
4.2.6 LIFETIME ESTIMATION 43
4.3 CORROSION MECHANICS.............................................................................................. 45
4.3.1 LAPO4 46
4.3.2 HASTELLOY C22 51
CONCLUSIONS AND RECOMMENDATIONS........................................................ 56
5.1 CONCLUSIONS .............................................................................................................. 56
5.2 RECOMMENDATIONS .................................................................................................... 58
WORKS CITED.............................................................................................................. 60
APPENDIX...................................................................................................................... 66
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A-1 HISTORICAL INDUSTRIAL CORROSION STUDIES .......................................................... 66
A-2 CORROSION DATA ...................................................................................................... 69
AISI 316 HIGH TEMPERATURE ACID 70
A-3 SEM/EDS................................................................................................................... 72
SAMPLES TO BE TESTED 72
A-4 RECOMMENDATIONS FOR FUTURE WORK ................................................................... 75
LANTHANUM PHOSPHATE 75
A-5 ALLOY COMPOSITION ................................................................................................. 77
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List of Tables
Table 1. Physical properties of lanthanum phosphate ..................................................... 10
Table 2. The average composition of the process gas in the furnace .............................. 18
Table 3. Typical contaminants in refinery grade sulfuric acid ......................................... 28
Table 4. Average post combustion furnace gas composition .......................................... 37
Table 5. Statistical analysis of variability of corrosion test ............................................. 38
Table 6. Boiling acid corrosion test comparison of Al2O3 and Hastelloy C22............... 43
Table 7. Specific details of boiling acid corrosion tests on Hastelloy C22 ..................... 69
Table 8. Specific details of boiling acid corrosion tests on LaPO4.................................. 69
Table 9. Specific details of boiling acid corrosion tests on Al2O3................................... 69
Table 10. Specific details of high temperature field tests of materials in the furnace..... 70
Table 11. Corrosion information on the AISI 316 immersed in 99 wt. % H2SO4 ........... 71
Table 12. Details of coupons SEM/EDS analyzed .......................................................... 72
Table 13. Industrial utilized alloy compositions for nozzles ........................................... 77
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List of Figures
Figure 1. Typical spent gun design [14]. ........................................................................... 2
Figure 2. Spent acid injection gun orientation into the furnace. ........................................ 3
Figure 3. Crystal structure of monazite LaPO4 [47]. ....................................................... 11
Figure 4. La2O3 - P2O5 phase diagram. ............................................................................ 13
Figure 5. Vaporization losses of P2O5 from La(O3)3 and LaP5O14. ................................. 14
Figure 6. Location of nozzle corrosion. ........................................................................... 19
Figure 7. Nozzle after an in-service failure. .................................................................... 19
Figure 8. Diagram of combustion furnace used to simulate process. .............................. 20
Figure 9. Firing schedule for the LaPO4 coupons............................................................ 22
Figure 10. XRD of calcined LaPO4 powder. ................................................................... 23
Figure 11. Standard XRD pattern of monazite LaPO4 [71]. ............................................ 23
Figure 12. EDS signature of the commercial LaPO4 calcined at 700°C.......................... 24
Figure 13. EDS signature of LaPO4 synthesized in this work. ........................................ 24
Figure 14. PVA burnout schedule for our LaPO4 coupons.............................................. 25
Figure 15. Illustration of boiling acid corrosion apparatus.............................................. 26
Figure 16. Dependence of boiling point of sulfuric acid on its strength [7].................... 27
Figure 17. CTE of LaPO4................................................................................................. 30
Figure 18. Comparative TGA/DSC plots for the LaPO4 samples. .................................. 31
Figure 19. TGA/DSC analysis with three consecutive heat cycles. ................................ 32
Figure 20. Corrosion results for Al2O3, LaPO4 and Hastelloy C22 in the furnace. ......... 36
Figure 21. Consistency of the corrosion rate for Hastelloy C22 in 99 wt. % H2SO4. .... 38
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Figure 22. Hastelloy C22 corrosion rates as a function of acid strength. ........................ 40
Figure 23. Results of Al2O3 corrosion in 90 and 99 wt. % refinery grade sulfuric acid.. 41
Figure 24. Time for complete dissolution of LaPO4 coupons. ........................................ 42
Figure 25. Estimation of nozzle failure time for Hastelloy C22...................................... 44
Figure 26. Comparison of nozzle failure time for alumina and Hastelloy C22.............. 45
Figure 27. LaPO4 EDS scan broad view 1000 µm [61]................................................... 47
Figure 28. LaPO4 EDS scan grain boundary zoom view 100 µm [61]............................ 47
Figure 29. EDS scan of LaPO4 [61]................................................................................. 48
Figure 30. SEM/EDS analysis of as-received Hastelloy C22 [61]. ................................. 53
Figure 31. EDS Scans of Hastelloy C22 corrosion tested in 90 wt. % sulfuric acid. ...... 54
Figure 32. A 36 mild steel tested in room temperature spent sulfuric acid. .................... 67
Figure 33. AISI 304 tested in room temperature spent sulfuric acid. .............................. 67
Figure 34. AISI 316 tested in room temperature spent sulfuric acid. .............................. 68
Figure 35. Corrosion rate of AISI 316 in high temperature 99 wt. % H2SO4.................. 71
Figure 36. Element composition of the alloys considered............................................... 77
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Chapter 1
Introduction
1.1 Sulfuric Acid Regeneration Process
Sulfuric acid is one of the largest produced chemicals by weight in the world.
Sulfuric acid is used in nearly every industry, including, agro-products, mining, paper and
pulp, steel production, water treatment, surfactants and soaps, plastics, petrochemicals
and refining. Its uses are so broad and diverse that a country’s production of sulfuric acid
was once used as an economic indicator [1, 2]. The sulfuric acid regeneration process
considered in this study is sulfuric acid from alkylation units on refineries.
The sulfuric acid is used as a liquid catalyst to convert olefins to alkylate in the
alkylation process. Alkylation uses primarily the C3 – C5 olefins from the fluid catalytic
cracker unit, to produce a valuable product, alkylate, a blending component used in the
gasoline pool, whose the percentage in the pool varies with season and the region.
Alkylation plants using sulfuric acid often consume 0.3 - 0.6 pounds acid per gallon of
alkylate, and produce more than 500,000 barrels alkylate per day in the United States
alone. Therefore, about 10 million pounds of sulfuric acid are consumed each day in the
refineries [2-13]. This acid must be regenerated for repeated use.
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The acid is regenerated through a thermal decomposition process. In this process
the acid is injected into the furnace and heated to 980°C, where it is decomposed. The
resulting gas stream is recycled through a modified contact process. The process,
however, is quite corrosive and warrants development and use of corrosion-resistant
materials for injection nozzles as well as their periodic maintenance.
1.2 Injection Nozzles
In a typical decomposition process, the nozzle atomizes the spent acid and sprays
the atomized fluid into a furnace operating in the range of 980-1260°C. A properly
designed furnace and gun configuration recesses the gun in the refractory and cools the
gun with atomizing air. This keeps the gun temperature below about 540°C.
Figure 1. Typical spent gun design [14].
The spent acid guns inject the acid in a radial pattern around the centerline of the
furnace near the front where the burner is located, as shown in Figure 2 below. It is
desired to keep the spray zone of each gun from colliding with the flame which results in
flame quenching causing turbulence and soot formation. The turbulence within the
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furnace can also create moving hot zones. If a hot zone occurs near a spent gun port, it
can back spray acid onto the gun and overheat it, causing rapid nozzle failure.
Figure 2. Spent acid injection gun orientation into the furnace.
Once the acid is atomized within the furnace, it is rapidly heated to the
decomposition temperature. This is a highly endothermic reaction that requires large
amounts of fuel for heating. The reaction results in sulfur dioxide gas as a desired
product for the regeneration process. The reaction occurring in the furnace is described
below.
H2SO4 (l) � SO2 (g) + H2O (g) + ½ O2 (g) ∆H˚Decomposition +202 kJ/ mol
Currently, the material of choice for the nozzles is Hastelloy C22. This alloy has
shown great resistance to corrosion in the manufacturing of sulfuric acid compared to the
traditional stainless steels such as 304, 316 and alloy 20. Hastelloy C22 is more robust
for use in high corrosion areas. Other acid regeneration processes in the esterfication
industry have reported using Hastelloy B2 (a nickel-molybdenum alloy) with similar
results [15]. Alloy compositions are listed in appendix A-5 for comparison [16-19].
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1.3 Motivation
The required energy to heat and decompose the spent sulfuric acid is the main
cost associated with the regenerative operations. Great effort is put into optimizing the
process to reduce the amount and cost of fuel required for this purpose. A major fraction
of the fuel is consumed in the atomization of the spent acid in the furnace. Specially
designed guns and injection systems have received considerable attention and are covered
in multiple patents [14, 15, 20-22]. These designs, however, offer improvements only if
the nozzles are in working order; corrosion of the nozzles greatly limits the effectiveness
of these systems. Operators must constantly monitor each gun’s performance and
quickly decommission or change poor performing guns to minimize adverse effects on
the process. Considering an average gun lifetime of 3 months and 10 – 20 guns per
furnace, frequent weekly nozzle failures are observed.
In addition to the monetary losses due to frequent injection nozzle failure due to
wasted fuel, furnace refractory damages also occur; inadequately atomized acid collects
as pool on the refractory. The pooled acid slowly evaporates and burns off causing
advanced corrosion to the refractory, whose replacement is expensive.
Enhancement of corrosion resistance for sulfuric acid injection nozzles would
greatly improve the regeneration process. Long-lasting nozzles would minimize
refractory damage and reduce operating costs through fuel savings, thus adding overall
reliability to the process.
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1.4 Research Focus
The currently used injection nozzles materials do not adequately withstand the
corrosion of the sulfuric acid regeneration process resulting in frequent and costly nozzle
failures. The development of an improved material for the nozzles could reduce the
impact nozzles have on the process efficiency. With this problem at hand in sulfuric acid
regeneration plants, the present work pertains to the search for and development of
alternative somewhat inert and more robust ceramic materials suitable for the fabrication
of atomizing nozzle. Lanthanum phosphate monazite was considered such a possible
material based on its excellent physical, thermal and chemical integrity under conditions
generally encountered in the acid regeneration furnaces. The research was focused on the
aspects of material degradation as a corrosion and process specific parameter.
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Chapter 2
Literature Review
2.1 Lanthanum Phosphate Monazite
Due to its remarkable physical and chemical properties, lanthanum phosphate
monazite has been considered a potential material for spent nuclear fuel storage, and
corrosion resistant structural material in turbines and fuel cells, due to its machinability.
Lanthanum and other rare earth oxides are readily available and are quite
inexpensive[23]. Among various rare-earth compounds, lanthanum phosphate (LaPO4)
has been proven to be the most appropriate due to its high melting point, chemical
stability, and inertness towards reaction with combustion gases at high service
temperatures [24, 25]. Lanthanum phosphate also interacts benignly with traditional
ceramics in a manner that improves the system characteristics exhibiting favorable
material properties[24, 26-34].
2.1.1 Combustion Applications
In addition to improving the mechanical properties, lanthanum phosphate
monazite offers refractory properties as well, that are useful in extreme environments.
Applications such as coatings for aircraft engine turbines or heat-resistant tiling for space
vehicles experience temperature extremes. Current materials involved in these
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applications utilize a composite of lanthanum phosphate with other ceramics with the
former being major constituent [35]. Selection of material for developing nozzles for
sulfuric acid regeneration also requires the ability to withstand high temperatures.
Lanthanum phosphate monazite is an attractive alternative oxidation-resistant
candidate for constituting a ceramic matrix composite (CMCs) in the intermediate and
high temperature regime of turbines. It performs better than the traditional carbon or
boron nitride fiber matrix interfaces, due to its refractory nature and superior thermo-
mechanically stability than that of alumina or mullite. Crack deflection, fiber pushout
and mechanical tests data suggest that lanthanum phosphate bonds weakly with other
oxides [36]. These properties with the combination of cleavage, twinning and dislocation
glide make the material exhibit significant plasticity, thus allowing the material to be
machinable. In addition to excellent high temperature oxidation resistance and increased
toughness, lanthanum phosphate exhibits good corrosion resistance in environments
containing sulfur and vanadium salts [23], which are present in carbon based fuels. The
salts are formed during fuel utilization many of which occur in molten state, and become
entrained in the gas stream. The molten salts impinge and condense on the turbine blades
thereby causing localized corrosion. Such corrosive impurities also exist in spent sulfuric
acid and are the likely source of nozzle corrosion. A material with increased resistance to
the sulfur and vanadium salts would add another layer of protection to the atomizing
nozzle.
Rare-earth phosphates (collectively known as monazites) are stable and
compatible with alumina up to1750°C in air and melt congruently in the vicinity of
2000°C. Lanthanum phosphate is sufficiently weak to allow for crack deflection and
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debonding at the fiber/matrix interface; its coefficient of thermal expansion (CTE) is
9.6x10-6 deg
-1 which is ~25% higher than that of alumina [36]. A combination of all the
above-stated favorable properties makes lanthanum phosphate a good candidate material
for nozzles in sulfuric acid regeneration furnace.
2.1.2 Machinability Characteristics
The essential requirement for a ceramic to be considered for nozzle fabrication is
its machinability. The guns are dropped, slammed into the burner port and adjusted with
pipe wrenches and hammers during operations. A brittle ceramic would never last the
rigors a nozzles experiences. A machinable ceramic therefore, would offer better
resistance to the harsh handling of spent acid guns. Also, nozzles tend to plug from debris
in the spent acid; other failures of the gun parts require quick field maintenance using
some of the above mentioned heavy-duty tools. Specialty ceramics and advanced
coatings are generally not recommended in the industry; a nozzle made out of machinable
ceramic having properties like a metal nozzles would be preferred. In the light of this
and the above-mentioned factors, a nozzle made out of a machinable ceramic would
increase the likelihood of implementation of new nozzle made out of lanthanum
phosphate.
Machining is an inevitable requirement for the flexible use of advanced ceramics,
especially structural ceramics. However, the extremely high hardness makes conventional
machining very difficult or even impossible in the case of ceramics. Generally, two
methods are used for improving the machinability of ceramic materials. One is the
structural designing, where machinability of ceramics is optimized by adjusting the phase
distribution, porosity and microstructure [37]. The second method is by introducing a
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weak interface phase or layered- structure material in the matrix, which facilitates crack
deflection during machining, such as mica containing glass-ceramics [34].
Early attempts to make lanthanum phosphate machinable involved its composite
with Al2O3. Fracture energy measurements have shown that Al2O3/LaPO4 interface is
weak enough (compared to Al2O3/Al2O3 interface) to satisfy the He and Hutchison
debonding criteria for bi-material interfaces [30]. There were also multiple dislocations,
dislocation networks and subgrain boundaries inside the Al2O3 grains and between
Al2O3/LaPO4 grains. This type of structural development is responsible for active plastic
deformation that occurs within the Al2O3 grains through grain dislocation. Due to the
weak bonding of Al2O3 and LaPO4 and soft layered phase in LaPO4, this composite can
be easily machined with cemented carbide drills instead of conventional diamond tools
[37].
Davis et al. [24] demonstrated that the reason for LaPO4 to exhibit excellent
machinability is associated with the deformation bands observed within its individual
grain, which is similar to that of dislocations, twinning and martenistic transformation of
other ceramic materials [37]. Since, LaPO4 grains are weak, fracture mode is mainly
transgranular. Multiple dislocations and dislocations networks occur inside the LaPO4
grains. This suggests active plastic deformation via grain dislocation [37]. As stated
above, LaPO4 possesses a layered crystal structure, which can be readily delaminated due
to its low cleavage energy, leading to fracture propagation parallel to the layer plane.
Thus, crack deflections, branching and blunting during machining of layered LaPO4 help
to prevent macroscopic fractures from propagation beyond the local cutting area [34],
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leading to the belief that it would function well as a machinable ceramic nozzle in the
sulfuric acid regeneration plant.
2.1.3 Physical Properties
The reported physical properties of LaPO4 were thoroughly reviewed to ensure
that the material could comply with the requirement of the intended application, viz., the
sulfuric acid regeneration plant. Some consideration for developing a nozzle from
ceramic materials must be taken into account, such as: (1) high melting point, (2) absence
of phase transformation up to the operating temperature, (3) low thermal conductivity, (4)
chemical inertness, (5) comparable thermal expansion similarity with metallic nozzle, (6)
adequate toughness to allow machining and, (7) high strength to withstand operating
pressures and flows [23, 38-40]. Typical values of some of the physical properties of
lanthanum phosphate are shown in Table 1.
Table 1. Physical properties of lanthanum phosphate [23, 41]
Property Value
Melt point (°C) 2070
Thermal conductivity (W m-1 K
-1) 1.8
Coefficient of Thermal Expansion (K-1) 10.5 x 10
-6
Young’s Modulus(GPa) 133
Poisson’s ratio 0.28
Heat Capacity @ 25°C (J K-1 mol
-1) 101.28
Lanthanum phosphate crystallizes in two modifications: the rhabdophane-type
hexagonal LaPO4*0.5H2O and the monazite-type monoclinic LaPO4, the later being
achieved either through ball milling the LaPO4*0.5H2O powder for extended period or
calcining at temperatures above 600°C [42].
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LaPO4 (along with ScPO4 and YPO4) is a member of mineral group ABO4, which
includes silicates such as zircon (ZrSiO4), thorite (ThSiO4, tetragonal), huttonite (ThSiO4,
monoclinic), and coffinite (USiO4). Depending on the size of A-site cation, the ABO4
minerals crystallize in either the lanthanum phosphate monazite or zircon type motifs
[43-46].
LaPO4 crystallizes in a P21/n symmetry with four formula units in the unit cell.
Phosphorous is four-fold coordinated with oxygen in a distorted tetrahedral environment.
Lanthanum is nine-fold coordinated with oxygen in an unusual arrangement: five-fold
coordination with oxygen along a plane perpendicular to the c axis and four-fold
coordination with oxygen along the plane parallel to c (two oxygen atoms above and two
below the ab plane). It is geometrically described as a framework of LaO9 polyhedra and
PO4 tetrahedra alternating in 3-D. These fundamental blocks interpenetrate each other
and share oxygen atoms at the corner [27, 43-46].
Figure 3. Crystal structure of monazite LaPO4 [47].
LaPO4 like other ceramics has a direct relationship with density and corrosion
resistance. Increasing the density of a ceramic decrease pores and voids within the
ceramic body, decreasing the overall surface area. Therefore, LaPO4 corrosion resistance
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depends on the sintering conditions, as this control ceramic microstructure and density.
It has been found that increasing the sintering temperature from 900 to 1300°C resulted
in a decrease in pore volume fraction and increase in pore diameter from ~8 to ~25 nm.
Extended soaking at 1200°C transforms the defective, porous, and poorly crystallized
grains into small (40 nm diameter), well-crystallized ones with low level of porosity;
soaking for 100h at 1200°C caused grains to grow to ~100 nm in diameter with further
reduction in porosity [48]. Density of LaPO4 and its composites decrease with increase
in soak time. This is due to the concomitant increase in the grain size upon long-term
sintering [49].
2.1.4 Stoichiometry
To achieve optimum properties, LaPO4 must be formed with a 1:1 ratio of La: P.
Small deviations from stoichiometry change its solidus temperature from 2070°C to
1580°C on the La-rich side and to P-rich side at 1050°C [37, 50]. LaP3O9 decomposes to
LaPO4 with loss of P2O5 above ~875°C and becomes amorphous in the range of 1050 –
1225°C (the reported melting point of LaP3O9 is 1050°C). Therefore, without
appropriate phosphorous removal, samples sintered near or above the melting point of
LaP3O9, will be phosphate-rich amorphous phases, and may escape detection by XRD.
This phosphate could exist at grain boundaries of LaPO4 [51, 52].
The residual secondary phase hydrogen-phosphate and corresponding lanthanum
trimetaphosphate may impact the LaPO4 sintering in two ways. First, it decreases the
sintering temperature. This parameter could also be taken into account to explain better
sinterability of powders containing trimetaphosphate. Second, it promotes grain growth,
thereby decrease in surface area. Powders containing trimetaphosphate have greater
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initial surface area (SA ~ 32 m2g-1) than pure LaPO4 (SA ~ 17.5 m
2g-1). The grain
growth takes place with rapid grain boundary migration whereby the grain boundaries get
separated from the pores. To achieve high densification, this phenomenon must be
suppressed for it leads to intragranular pores inhibiting sintering. This detrimental effect
appears particularly important when trimetaphosphate present to the extent of 3.1%, only
78% of the theoretical density is reached [52].
Figure 4. La2O3 - P2O5 phase diagram [53].
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Figure 5. Vaporization losses of P2O5 from La(PO3)3 and LaP5O14 [53].
Considering La2O3-P2O5 phase diagrams, La(PO3)3 decomposes into LaPO4 with
incongruent melting in the range 1050-1235°C. This produces a phosphorous oxide rich
liquid and P4O10 gas. The presences of the secondary liquid phase may explain the
decrease of sintering temperature but not without grain growth [52, 53]. The off-gassing
of phosphorous pentoxide dimer threatens to damage sintering equipment during
processing. In addition, many different forms of lanthanum (LaPO4*0.5H2O, LaP3O9,
La2O3, La(PO3)3, and La(OH)3) existing greatly alter the ceramics properties. This will
affect the materials performance in high temperatures and will compromise its integrity.
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2.2 Microwave Sintering
The LaPO4 samples synthesized and employed in this study were sintered using a
microwave, with the aim to produce a dense nonporous ceramic body to enhance the
corrosion resistance. The benefits of microwave energy in thermally activated processes
stem from the specificity of energy absorption. Contrary to other conventional methods,
microwave energy is unique and transforms into heat within the material thus altering the
heating properties and greatly reducing process times [54-56].
Microwave processing also maximizes the mechanical properties of the ceramic
that would not be fully attained by traditional methods. It enables the ceramic to obtain
higher degree of densification and improve the intergranular structure and makes the
ceramic less susceptible to acid penetration and grain boundary dissolution. Both these
attributes contribute to improved resistance to corrosion and nozzle performance.
In conventional furnace heating, energy is transferred to the materials by thermal
electromagnetic radiation, with its maximum intensity being in the infrared range. The
penetration depth of infrared radiation is very small in a majority of solids. Therefore,
energy deposition is localized within a thin layer near the surface of materials. As a
result conventional heating essentially depends on heat transfer from the hotter near-
surface region to the colder bulk of the material [54-56].
Microwave heating on the other hand is based upon the capacity of a material to
absorb the electromagnetic energy. The absorption in this instance is assisted by
employing the hybrid heating scheme. This involves introduction of additional heat
sources into the system. These sources are microwave-absorbing objects (susceptors),
from which the microwave-generated heat is transferred to the low-loss material
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undergoing processing. The heat is deposited directly inside the sample, and the heating
rate is limited only by the power of the microwave source. The heat is dissipated to the
environment through the surface. Therefore, the temperature inside the sample is always
higher than on the surface. This microwave-specific temperature distribution is known as
an inverse temperature profile [54-56].
At elevated temperatures, microwave absorption in most materials grows sharply,
primarily due to an onset of another absorption mechanism. This is characteristics for
both ionic (Al2O3, ZrO2) and covalent (Si3N4, AlN) solids. A sharp increase in the
microwave loss begins at temperatures of about 0.4-0.5 Tm (where Tm is the melting
temperature of the material). In this range the bonds between ions in ionic crystals start
to break, and the electrons in covalent materials begin to populate the conduction bands.
A correctly designed susceptor system will provide heating at the initial stage, and reflect
most of the power at high temperatures when microwaves are absorbed directly by the
material undergoing processing [54-56].
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17
Chapter 3
Experimental
3.1 Experimental
3.1.1 Process Conditions
A number of simulated tests were conducted under conditions close to those
experienced by the sulfuric acid regeneration nozzles during service. The observations
were used to determine how the spent acid gun interacted with the incineration process
within the furnace. The guns were observed through downstream view ports, a video
camera and empty gun ports. These observations established that if the spent acid gun
were installed as designed, each gun would experience similar conditions and a standard
set of conditions were experienced by each spent acid gun.
The employed variables were temperature, gas composition and flow
characteristics. The operating temperature was determined by type-K thermocouple
inserted alongside a spent gun. The thermocouple was placed on the nozzle, but did not
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18
come in contact with the acid stream. The nozzle operated reasonably in the temperature
range of 600 –1000°C, preferably at 700°C. The gas composition was determined
through inline process sensors and the wet chemistry method known as the Orsat 1.
Table 2. The average composition of the process gas in the furnace
N2 H2O SO2 CO2 O2 SO3
55% 25% 10% 8% 2% <1%
Over fifty failed nozzles were collected from two different sites and analyzed;
each failure was found to be the result of localized corrosion on the bottom rim of the
nozzle. This confirmed that each gun was exposed to similar conditions and that a unique
mechanism was responsible for the failure. The corrosion led to a small hole at the
bottom rim of the nozzle which grew in size with time. The hole bypassed spent acid
around the atomizing chamber and injected spent acid as a stream into the furnace.
1 Orsat - is for analysis of process gas samples to determine CO2, O2 and sometimes CO concentrations
from fossil fuel emission sources. A liquid filled leveling bottle moves the integrated sample through a
graduated glass burette and absorption pipettes containing absorbing reagents. The resulting changes in
volume measure percent of O2 , CO2 and CO. The burette is water jacketed for temperature stability 57.
Apex Instruments, I. Method 3 Orsat Analyzer. 2002 [cited 2008 1-10-2008]; Available from:
http://www.apexinst.com/products/orsat.htm
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19
Figure 6. Location (highlighted in grey) of nozzle corrosion.
Figure 7. Nozzle after an in-service failure.
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20
The spent acid pooled at the bottom rim of the nozzle was the source of the
localized corrosion. This was verified through visual observation of the operating guns.
The turbulence in the furnace due to high flow rate caused the spent acid to pool at the
bottom of the nozzle in a cyclic pattern, alternating between acid gain and acid loss.
During acid gain the furnace flow would redirect atomized acid back towards the nozzle,
causing it to collect on the bottom rim. A slight change in the furnace conditions would
not allow the atomized stream to collect on the nozzle. The static pool would therefore
boil off.
3.1.2 Boiling Acid
For the evaluation of how the cyclic pooling of acid affected the corrosion
process, a bench-top combustion furnace (Figure 6) was employed. 99 wt. % acid in a
small crucible was placed in the furnace and heated to 650°C until the acid started to boil.
The temperature was then lowered to 500°C and held steady for 30 min.
Figure 8. Diagram of combustion furnace used to simulate process.
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21
This heating interval increased the volume of the acid and decreased the acid
strength. The acid strength decreased to < 90 wt. %, indicating that the hygroscopic acid
absorbed the water produced from combustion and diluted the acid pooled collected at
the bottom of the nozzle. This ameliorated the corrosion rate significantly as the weaker
acid was found to be much more corrosive.
3.2 Synthesis of LaPO4
3.2.1 Powder Synthesis
The lanthanum phosphate (LaPO4) powders were synthesized by reacting
phosphoric acid and lanthanum oxide (La2O3) in a continuously stirred de-ionized water
bath. Phosphoric acid was reagent grade 85% orthophosphoric acid JTBaker
(Phillipsburg, New Jersey) and La2O3 (99.99% purity) was purchased from Molycorp
(Englewood, Colorado). For the synthesis, phosphoric acid was first diluted with
distilled water bath, followed by the slow addition of La2O3 to the aqueous acid. The
reactants were added in the proportion of La to P molar ratio of 1:1 in order to yield
LaPO4 as the final desired product per the following scheme:
2La2O3 + 3H3PO4 � 2LaPO4*0.5H2O + LaPO4 + La(OH)3 + 2H2O
The hydrated form of LaPO4 must be calcined to remove the attached water.
Once the water is removed through dehydration LaPO4 exists in the monazite phase.
This research illustrates that the initial calcination removes the majority of the water, but
minute amounts of water are reabsorbed during cool downs. Also, it was found that the
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22
La(OH)3 residual bi-product is removed during the initial sintering and the resulting
weight loss does not reoccur. These findings are discussed further in chapter 4 Figure 17.
The undesired impurity (La(OH)3) must be removed through further processing.
As La2O3 is added to the diluted phosphoric acid, the reaction proceeded
immediately via precipitate formation. The solution is constantly stirred during the
reaction and continued for 24 additional hours to ensure completion of the reaction. The
precipitate was allowed to settle, washed several times with de-ionized water until the pH
of the decanted water was close to 7. The hydrated precipitate was calcined in air using
the following heating schedule
Figure 9. Firing schedule for the LaPO4 coupons.
This firing schedule helped in water removal from hydrated lanthanum phosphate
and its transformation into the monazite form. The X-ray diffraction peaks in the
calcined samples (Figure 8) conformed to those of LaPO4 (JCPDS#320493; monazite
structure) as shown in Figure 9.
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23
Position [°2Theta]
20 30 40 50
Counts
0
100
200
300
400
LP700
Figure 10. XRD of calcined (700°°°°C/4h) LaPO4 powder.
Figure 11. Standard XRD pattern of monazite LaPO4 [71]
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24
Figures 10 and 11 show the EDS signatures in the commercial monazite from Alfa Aesar
and that synthesized in this work, both caclined at 700°C. As can be seen, the two EDS
scans are very similar.
Figure 12. EDS signature of the commercial LaPO4 calcined at 700°C.
Figure 13. EDS signature of LaPO4 synthesized in this work.
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25
3.2.2 Sintering
The calcined lanthanum phosphate powders were ball-milled for 24h as aqueous
slurry using zirconia spheres as the milling media, dried in a vacuum oven and mixed
with 2 wt.% of polyvinyl alcohol (PVA). The powder was uniaxially pressed into pellets
(2cm x 3.5cm) under a pressure of 240 kPa, followed by cold isostatic pressing (CIP)
using a force of 71.2 kN.
The CIPed samples were first fired up to 250°C in a traditional electric furnace to
burn out the organic binder (PVA) prior to microwave (MW) sintering. This is a required
step for the microwave unit because the organic vapors could cause arcing and damage
the unit. A slow ramp rate was used during the binder burnout, as faster rates resulted in
cracking of the pellets. The heating schedule was as follows:
Figure 14. PVA burnout schedule for our LaPO4 coupons.
The samples were sintered using a ThermWave Model III MW Power Unit
microwave furnace Ceralink Inc. (Troy, New York). It operates at 2.45 GHz with two 50
gram silicon carbide susceptors. The samples were heated to 1575°C in about 45
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26
minutes, held for 15 min., and allowed to cool to room temperature in the insulated box
[88]. While the unsintered samples were granular and porous, the sintered ones became
semi-glossy and quite dense.
3.3 Corrosion Test
3.3.1 Boiling Acid Experiment
As explained above, the location of nozzle failure was at the bottom where acid
would pool and boil off. Based on this failure mechanism, it was desired to reproduce the
conditions so that alternative materials could be tested prior to fabricating actual nozzles
from these compositions. The boiler apparatus was a 250 mL boiling flask with a water-
cooled reflux condenser attached. The candidate nozzle material sample was placed in
the flask and the acid was added to the flask, submerging the sample. A heating element
was then used to bring the acid to a boil.
Figure 15. Illustration of boiling acid corrosion apparatus.
The factors considered in the boiling unit were: the acid strength (99 and 90 wt.
%), materials (LaPO4, Hastelloy C22, & Al2O3), and the period of time the sample was
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27
subjected to boiling acid tests. The acid used in the boiling tests was refinery grade. 60
ml of the H2SO4 acid was used in all the tests; in the case of tests with acid of 90%
strength, the 99% acid was diluted with adequate amount of water. This was done to
standardize the amount of acid present in the solution regardless of strength.
All tests were conducted using a standardized protocol. The flask was cleaned
and dried before each test. The sample was placed in the flask and the acid was added.
The flask was then attached to a condenser tube which was then connect to cooling water
circulation. Finally, the heater was turned on; it took about 30 minutes to boil.
Figure 16. Dependence of boiling point of sulfuric acid on its strength [7].
The materials in the boiling apparatus are subjected to high temperatures based on
the boiling point of concentrated sulfuric acid. As seen from Fig 18, the 90 and 99 wt. %
sulfuric acid boil at about 260°C and 280°C, respectively. Though the boiling apparatus
operated at a constant acid strength, the nozzle however, experienced fluctuating strength
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28
during operation. This could expose the nozzle to temperatures in excess of 330°C,
which in turn could influence the corrosion rate significantly.
3.3.1 Acid Samples
The acid used for corrosion tests was taken at random in a 3 month span from a
sulfuric acid regeneration facility. Each aliquot was 350 ml and 99.25 (± 0.20) wt. %
taken from the same source point when sampling large shipments for refiners. In all, 15
samples were used. All the samples were stored individually and used at random. The
nature and concentration of contaminants in a typical fresh refinery grade sulfuric acid is
shown in Table 6.
Table 3. Typical contaminants in refinery grade sulfuric acid
Species SO2 Fe Nitric Cr Pb As Cd Hg Calcined Residue
mg/kg 50 20 10 1.0 1.0 0.50 0.05 0.05 100
Spent sulfuric acid was not used because it contains 4 – 7 wt. % hydrocarbon
carryovers from the alkylation unit, which tends to boil at around 60°C, foaming out of
the reflux unit and forming pumice-like solid substances [58]. This would inhibit the
simulation of the actual process occurring in the furnace (viz., a pool of acid collecting at
the tip of the nozzle and boiling without the formation of solid residue). It was assumed
that the atomization of the spent acid facilitated in the removal of most of the
hydrocarbon.
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29
Chapter 4
Results and Discussion
4.1 Material Properties of Lanthanum Phosphate, LaPO4
The material properties of LaPO4 were evaluated to determine if the material was
compatible with the service conditions of a nozzle. Measurement of the coefficient of
thermal expansion (CTE) and simultaneous TGA/DSC analysis were used to determine if
the material underwent unusual expansion, phase changes or chemical instabilities that
would compromise its structure while in service [23, 38-40]. Tests were also conducted
to verify if LaPO4 was machinable as reported.
4.1.1 Coefficient of Thermal Expansion
The coefficient of thermal expansion (CTE) was determined using a dilatometer
DIL 2016 STD (Orton, USA). The test coupon made from the commercial LaPO4 powder
procured from Alfa-Aesar, after calcining and sintering as described in Chapter 3. The
CTE measurements were done in air between 25 and 1125°C and the results are shown in
Figure 15.
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30
-35
-30
-25
-20
-15
-10
-5
0
5
10
25 225 425 625 825 1025
Temperature Deg. C
CT
E (
x 1
06 K
-1)
Figure 17. CTE of LaPO4.
As can be seen from Figure 15, between room temperature and 1100°C, the
ceramic expands by 0.75% during heating and contracts by 3% upon cooling of its
original linear dimension.
During thermal cycling, the expansion and contraction however, did not
compromise the structure of LaPO4 (within the operational temperature range of the
nozzles) since exceeding 1000°C in the regeneration process is uncommon. The LaPO4
nozzle must be jointed with a Hastelloy C22 gun body, which has a CTE value of 12.4 x
10-6 K
-1 below 500°C and 15.8 x 10
-6 K
-1 at 1000°C. Obviously, the CTE values for the
ceramic and the alloy differ, but this difference can be accounted for in the gun design.
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31
4.1.2 Thermal and thermogravimetric Analysis
Analysis by thermogravimetry and differential scanning calorimetry (TGA/DSC)
was conducted on the commercial and the lab-synthesized LaPO4 powders after
calcination. The analysis assisted in determining if the material experienced a phase
change or chemical instability within the temperature range of nozzle’s operation. The
synthesis process of LaPO4 powder was also analyzed using the TGA/DSC technique
analysis on both commercial and our samples. The results are compared in Figure 16.
0.985
0.987
0.989
0.991
0.993
0.995
0.997
0.999
0 275 550 825 1100
Temperature Deg. C
Weig
ht
Ch
an
ge
-0.6
-0.1
0.4
0.9
1.4
1.9
Heat
Flo
w (
W/g
)
Weight ChangeCommercial
Weight Change ThisWork
Heat Flow (W/g)Commercial
Heat Flow (W/g) ThisWork
Figure 18. Comparative TGA/DSC plots for the LaPO4 samples; our sample
contained 2 wt. % the binder (PVA).
The major weight loss was associated with the release and evaporation of water
absorbed during synthesis and storage [59]. Figure 17 shows the trend of weight loss and
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32
heat flow characteristics over several cycles. Again, the first heating cycle shows the
largest weight loss. The second weight loss was not due to dehydration but to residual
reactants and intermediate products decomposing or off-gassing upon heating. This
weight loss only occurred during the first heating cycle and no significant weight change
occurred in subsequent heating cycles.
Figure 19. TGA/DSC analysis with three consecutive heat cycles.
The heat flow analysis suggested that there were structural changes at around 200
and 850°C. The changes in heat flow rates were not large in magnitude and further
diminished and remained small over repeated cycles. Based on TGA/DSC analysis
results, it can be concluded that LaPO4 did not experience any drastic or unusual phase
change or chemical instability that would compromise the functionality of the ceramic in
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33
the intended application.
The TGA/DSC profiles in Figure 17 show certain distinction for the two samples
used here. The LaPO4 sample synthesized in this work and used for the analysis,
contained 2 wt% of PVA as binder and residual acid. Hence, it showed a weight loss of
0.013% compared to 0.003% in the case of commercial sample. PVA burn-off in our
sample is obviously the largest contributor to the observed large weight loss. The heat
flow peak at ~850°C is about 1W/g larger for our sample than in the case if its
commercial counterpart from Alfa-Aesar.
Possibly, the difference between the two TGA/DSC signatures of the samples was
due to the residual H3PO4 present and the secondary compounds that correspond with the
excess acid residue in our sample. Side reactions and undesired products were likely
formed when the reactants were mixed. Considering that excess H3PO4 existed, a
polytriphosphate phase could result and its presence could explain the observed peak at
about 850 °C. The polytrioxophosphate forms as the result of the following series of
reactions [59].
H3PO4(absorbed) � HPO3(adsorbed) + H2O(g)
2HPO3(ad) + LaPO4(s) � La(PO3)3(s) + H2O(g)
The net reaction being,
2H3PO4(absorbed) + LaPO4(solid) �La(PO3)3(s) + 3H2O(g)
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34
This last net reaction, potentially accounts for the peak seen at about 850°C. Between
1050 and 1350°C the triphosphate decomposes into LaPO4 and gaseous phosphorous
pentoxide dimer [59]:
2La(PO3)3(s) � 2LaPO4(s) + P4O10(liquid, gas)
A weight loss due to the release of P4O10 gas in this high temperature regime
accompanies the incongruent melting of La(PO3)3 [53, 59], accounting for the one-time
weight loss during the first heating step, especially at the higher end of temperature, and
the difference in heat flow characteristics of the two sets of LaPO4 samples. This
incongruent melt and weight loss follows the phase diagram of La2O3 – P2O5 illustrated
in chapter 3. Also, the vaporization of by-products is illustrated in the vaporization losses
of P2O5 from La(PO3)3 and LaP5O14. These figures are useful based on the consideration
of excess La or P.
4.1.3 Machinability
A small coupon of sintered LaPO4 was tested for its machinability. The coupon
was drilled using a carbide-tipped bit. The drill bit cut through the material resulting in
crisp defined edges and minimal chipping. A drill bit without carbide was attempted and
the material was cut through, but chipping and fracturing occurred to a small extent.
Hence, LaPO4 is machinable using carbide tools.
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35
4.2 Corrosion Tests
The sintered LaPO4 samples were tested in simulated conditions close to what a
nozzle would experience during service. The two modes of testing, viz., exposure to the
furnace gasses and boiling acid were used.
4.2.1 Field Test
The field tests were conducted to determine if the materials could be used in the
furnace. The leading factor in determining if they were usable was if each material
would retain the required structural properties to compose a nozzle. The coupons were
tested in conditions similar to those experienced within the furnace. The coupons were
placed in a carbon steel container and inserted into an unoccupied spent gun port while
the furnace was operating. The container eliminated direct flame contact and reduced
soot deposition. A hand-held type K thermocouple was periodically used to determine
the temperature within the container. The temperature fluctuated from 540 to 1050°C
depending up on the gas flow rates and flow patterns within the furnace. To normalize
these fluctuations, the samples were left in the furnace for a minimum of two days and
tested during typical plant operating conditions. This ensured each set would experience
very similar conditions.
The first field test used A 36 mild steel, AISI 316 stainless steel, Hastelloy C22,
Al2O3 and LaPO4 as the study materials in furnace gas corrosion experiments. After the
first run, A 36 mild steel and AISI 316 were eliminated from the test because the
corrosion in these two samples was too severe compared to other materials. The mild
steel and stainless steel appeared to carburize and developed brittle flaky coating on the
exterior surface that came off easily. Remaining tests used Hastelloy C22, Al2O3 and
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36
LaPO4. The corrosion rate of Hastelloy C22 alloy and the ceramics was comparable, but
the ceramics offered a slight improvement. Al2O3 showed the best resistance to high
temperature environment within the furnace.
Al2O3
LaPO4 (2%PVA)C22
0.00E+00
1.00E-06
2.00E-06
3.00E-06
4.00E-06
5.00E-06
6.00E-06
7.00E-06
1
Sample Material
Weig
ht
Ch
an
ge
(g
/hr)
Al2O3
LaPO4 (2%PVA)
C22
Figure 20. Corrosion results for Al2O3, LaPO4 and Hastelloy C22 in the furnace.
During the field tests conducted in the furnace only the alloys were greatly
affected and the source of corrosion appeared to be carburization. Carburization, a
corrosion process, affects steels and high-temperature alloys mostly at temperatures
above 900 °C. Ingress of carbon leads to the precipitation of stable carbides M23C6 and
M7C3 (M = Cr, Fe, Ni), with Cr as the main metal component. This precipitation causes
embrittlement, a volume increase of the carburized zone, cracking in the outer surface
and also loss of oxidation resistance. This kind of carburization can be widely suppressed
by protective oxide scales, but in cases of oxide failure it is controlled also by surface
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37
reaction and carbon diffusion kinetics [60]. This mechanism is viable based on the
temperature and composition of the furnace gas.
Table 4. Average post combustion furnace gas composition
N2 H2O SO2 CO2 O2
50% 27% 12% 10% 2%
Based on the results of the field tests it appears that Al2O3, Hastelloy C22 and
LaPO4 could withstand the furnace gas conditions. Based on the rate of nozzle failure
during operation, the hot gas corrosion is not the leading mechanism of failure. The field
tests in the furnace port showed that the leading cause of failure is boiling acid on the tips
of the nozzles.
The field test also established that these materials could withstand the thermal
shock during insertion into and removal from the furnace. The coupons were placed in
the furnace gun port without preheating or a controlled heating rate, resulting in a rapid
rate of heating. Once the test was concluded the samples were removed and air cooled.
The thermal stress from the rapid heating and cooling did not damage the coupons. This
showed that LaPO4 could withstand the typical procedure of commissioning and
decommissioning of the gun.
4.2.2 Consistency of Boiling Acid Test Procedure
The first set of boiling acid corrosion tests was run to determine the variability of
the test method. This assisted in determining how the testing apparatus and the acid
samplings affected the outcome of the tests. All tests were run for approximately 28
hours (ranging from 24 – 32 hours) with coupons of similar size and weight. Also, each
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38
of the Hastelloy C22 coupons were cut from the same plate intended for construction of a
piece of equipment.
-0.02500
-0.01500
-0.00500
0 10 20 30 40 50
Time (hours)
Ma
ss
Lo
ss
(g
/cm
2)
Figure 21. Consistency of the corrosion rate for Hastelloy C22 in 99 wt. % H2SO4.
Based on the experimental data shown in Figure 19 following statistics were
calculated for the variance tests (Table 5).
Table 5. Statistical analysis of variability of corrosion test
Property Value
Average Time (h) 27.7
Average Corrosion Rate (g /cm2 /h) 0.006
Standard Deviation of Corrosion Rate 0.0026
Median Corrosion Rate (g /cm2 /h) 0.0059
Average Surface Area (cm2) 6.56
Standard Deviation Surface Area 0.33
Number of Tests 6
Acid Selection Random
Acid Strength (% wt. H2SO4) 99.25±0.25
Despite slight differences in coupon size and surface area the test results were
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39
fairly consistent and reproducible. The boiling acid apparatus provided an accurate
simulation of the field conditions of the nozzle.
4.2.3 Hastelloy C22 Boil Tests
Hastelloy C22 corrosion tests were conducted to develop a mode of comparison
for the new materials under consideration. It was known that advanced corrosion was
occurring, but the rates of corrosion were not known. The boiling test rates provided an
estimation of corrosion rates during operation. Based on protocol, the acid could be
between 87 – 99 % wt. H2SO4, but in common practice the acid would be close to 90 – 99
% wt. H2SO4. For this reason the tests were conducted with 99 % wt. H2SO4 and 90 %
wt. H2SO4, so as to cover a broad ranger
In the case of Hastelloy C22, the acid appeared transparent (clear water) initially
and proceeded to become milky light green in color. For the longer tests, sludge began to
build up at the bottom of the container. The alloy would appear burnt, transforming from
a shiny metallic luster to dull grayish black; bubbles of H2 were also produced. The
longer the coupon was in the acid the darker it became. The dull grayish black coloration
was only on the surface; scoring would reveal a shiny layer directly beneath the surface.
Figure 20 illustrates that the weight loss is linear on a per surface area per time basis.
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40
-0.006
-0.005
-0.004
-0.003
-0.002
-0.001
0
0 50 100 150 200
Time (hours)
We
igh
t lo
ss
(g/c
m2/h
)
99 %wt.
90 %wt.
Figure 22. Hastelloy C22 corrosion rates as a function of acid strength.
As can be seen, the corrosion of the Hastelloy C22 coupons was much more rapid
in 90 wt. % acid than in 99 wt. %. This was evident by the discoloration of the acid,
taking on a much darker green hue. The discoloration of the surface was dark for the
shorter duration test, but the longer duration test showed localized spots that were pitted
and shiny. The testing of Hastelloy C22 in sulfuric acid established a standard for future
materials and assessed the variance of different testing method. It also verified that 90
wt. % was much more corrosive than the 99 wt. % and that the corrosion rate was directly
related to the time of exposure.
4.2.4 Al2O3 Boiling Acid Tests
Alumina (Al2O3) was also tested in boiling sulfuric acid. High density
machinable alumina ceramic (99.99% pure) was purchase from McMaster–Carr
(Cleveland, USA) and cut into 5/16″ x 1″ coupons. Without a diamond blade wet saw, the
material fractured and chipped. It was apparent that to compose a nozzle with this
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41
material it would have to be molded and net-formed prior to sintering.
-6.00E-04
-5.00E-04
-4.00E-04
-3.00E-04
-2.00E-04
-1.00E-04
0.00E+00
1.00E-04
0 20 40 60 80 100 120 140
Time (h)
We
igh
t lo
ss
(g
/h)
99 wt.% H2SO4
90 wt.% H2SO4
Assumed this is a balance
measuring error and not an
actual gain in mass.
Figure 23. Results of Al2O3 corrosion in 90 and 99 wt. % refinery grade sulfuric
acid.
Despite the foreseen difficulties in fabricating a nozzle, the alumina ceramic
exhibited promising results in the corrosion tests. The influence of acid on alumina
ceramic was not discernable as the coupons appeared unaffected. The acid was clear and
transparent before and after the test. The alumina did not exhibit any of the common
characteristics of degradation as the other samples did, such as breaking off, discoloration
of acid and the sample surface, or acid absorption into the material.
4.2.5 LaPO4 Boiling Acid Tests
Many boiling acid tests were conducted on LaPO4 during the determination of the
optimal synthesis route for LaPO4, which was an iterative process. A batch would be
made, calcined, sintered and then tested in the boiling acid apparatus. Based on the
observations, changes to the synthesis process were made accordingly. The first rounds
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42
of tests considered the sintering temperature and soak-time. The samples sintered at
lower temperatures (900-1100°C) did not withstand the boiling acid and rapidly
dissolved. When the soak-time was extended, the longer duration did not have a benign
effect on the material resistance to the boiling acid. The sintering temperature was then
increased to 1300°C and PVA (2 wt. %) was included as a binder to aid densification
during sintering process. These changes made minimal improvements to the resistance
when compared to the samples sintered at 900 or 1100°C.
Finally, a sintering temperature of 1585°C resulted in a significant improvement
in the resistance to the boiling acid. The LaPO4 coupon sintered at 1585°C withstood 99
wt. % boiling acid for nearly 20h without PVA addition and over 100h in the case where
binder was added. This was a vast improvement from previous samples sintered at the
lower temperatures. Further tests employed longer sintering time, but this did not
increase the resistance noticeably.
0.0
20.0
40.0
60.0
80.0
100.0
120.0
Coupon
Ho
urs
LaPO4 No Binder
99%
LaPO4 2% PVA 99%
LaPO4 2% PVA 90%
LaPO4 without PVA
boiled in refinery
grade H2SO4 99 %wt.
LaPO4 w/ 2% wt. PVA
boiled in refinery
grade H2SO4 99 %wt.
LaPO4 w/ 2% wt. PVA
boiled in refinery
grade H2SO4 90 %wt.
Figure 24. Time for complete dissolution of LaPO4 coupons.
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43
As can be seen in this case also, the weaker acid degraded LaPO4 ten times faster
than the stronger acid did; LaPO4 with and without PVA dissolved in a consistent
manner. Each coupon would begin as a unified mass, but small pieces would break off.
The first pieces would be about a millimeter square and the subsequent debris would
progressively decrease in size to eventually become a fine grained powder.
4.2.6 Lifetime Estimation
Comparing the performance of Al2O3, Hastelloy C22 and LaPO4, in the
acid boiling unit, only Al2O3 showed appreciable resilience. LaPO4 did not show
promising results; the samples dissolved within a span of time that is too brief to function
as a nozzle. The results of the corrosion resistance between Hastelloy C22 and Al2O3 are
listed in table 6.
Table 6. Boiling acid corrosion test comparison of Al2O3 and Hastelloy C22
Material Acid wt. % g/cm2/hr g/hr
Al2O3 99 0 0
Hastelloy C22 99 1.50E-04 9.70E-04
Al2O3 90 6.38E-05 5.08E-05
Hastelloy C22 90 5.30E-03 2.10E-02
The resistance of alumina ceramic to the boiling acid was an order of magnitude
greater than that of Hastelloy C22; 10-5 as opposed to 10
-4 for
the 90 wt. % H2SO4. In the
99 wt. % acid, alumina did not experience weight loss, whereas the Hastelloy C22 alloy
had appreciable weight loss. The rates may not seem to be great, but considering that the
nozzle is used continuously (24 hours a day, 365 days a year) and considering that the
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nozzle body is extremely thin (about 0.635 cm) it can be destroyed in a very short period
of time.
Lifetime of a nozzle can be roughly predicted based on the size of a common hole
found in a failed nozzle. When the diameter of the hole reaches ~ 1 mm, the disruption of
spray becomes noticeable. Using this threshold, a time frame for failure can be estimated
using the corrosion rates determined in the laboratory. Figure 23 represents the estimated
failure time for a nozzle using the individual corrosion rates from 99 wt. % H2SO4 boil
tests, the average surface area (based on 1 mm diameter hole) and thickness of the nozzle.
The time taken by the acid to create a 1 mm diameter hole in the nozzle represents the
lifetime.
0.00
10.00
20.00
30.00
40.00
50.00
60.00
1 2 3 4 5 6 7 8 9 10 11 12 13 14
Individual Test
Lif
eti
me
(d
ay
s)
Figure 25. Estimation of nozzle failure time based on the corrosion rates for
Hastelloy C22 in 99 wt. % H2SO4.
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C22, 0.49
Alumina,
6.60
0.00
2.00
4.00
6.00
8.00
10.00
1
Tests
Lif
eti
me
(d
ay
s)
Figure 26. Comparison of nozzle failure time for alumina and Hastelloy C22
corrosion in 90 wt. % H2SO4.
The prediction of nozzle lifetime for the Hastelloy C22 in 99 wt. % H2SO4 agrees
well with the experiments in the field. The alumina is not represented in figures for 99
wt. % H2SO4 because there was no measurable corrosion. The Hastelloy C22 and
alumina in the 90 wt. % H2SO4 have a much reduced lifetime, but the alumina lasted
nearly 13 times longer than the Hastelloy C22. The predicted failure time represents the
time a nozzle will last when acid begins to pool on the nozzle; if pooling does not occur
the nozzle should last much longer. The results emphasize the importance of proper
operations and material selection.
4.3 Corrosion Mechanics
The results of the boiling acid tests and the furnace tests showed that the leading
cause of failure was corrosion due to acid boiling at the tip of the nozzle. Both
environments were corrosive and aided to the degradation of the material.
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4.3.1 LaPO4
The SEM/EDS analysis of the post-test samples shows that the corrosion
mechanism responsible for degrading LaPO4 originates at the grain boundaries. The
segregation of alumina to the grain boundaries is illustrated in Figure 26. Al2O3 is an
impurity phase present in LaPO4. It segregates to the grain boundaries but does not react
with the lanthanum phosphate [26, 29-31, 34, 35, 92]. During acid boiling, Al2O3 is
dissolved along with the grain boundaries and material loss occurs which increases with
time. This can be seen in Figure 25.
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Figure 27. LaPO4 our sample with 2 wt. % PVA sintered at 1575 °C, EDS scan
broad view 1000 µm [61].
Figure 28. LaPO4 our sample with 2 wt. % PVA sintered at 1575 °C, EDS scan
grain boundary zoom view 100 µm [61].
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The analysis of the sintered LaPO4 after exposure to the boiling 99 wt. % H2SO4
revealed that the acid and LaPO4 were reacting. The EDS pattern shown in Figure 27
identifies the major elements as lanthanum (La), oxygen (O) and sulfur (S). The scan did
not resemble the EDS scans of the coupon before the test.
Figure 29. EDS scan of LaPO4 laboratory synthesized and acid boil tested in 99 wt.
% H2SO4 [61].
Based on the EDS results it appears that the acid boiling removed the alumina
impurity and phosphate. The sample was not cross-sectioned and depth-profiled, so it is
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not known if this is a surface reaction or if the acid penetrated the pores and reacted with
the bulk of the ceramic.
The first phase of decomposition would be the removal of the phosphate group.
This could be accomplished in a reaction similar to the dissolution of phosphate glasses,
when glass-ceramics are reheated to temperatures above crystallization. In the case of
LaPO4 the residual carbon and acid within the bulk ceramic creates different phase
boundaries and promotes the dissolution of the boundaries, as seen in the SEM of the
corroded sample.
Within the bulk ceramic the following materials exist in some unknown
concentration.
LaPO4 ; La3PO7 ; La2O3 ; La(PO3)3
The impurities at the grain boundaries and the temperatures at which the acid boils could
greatly affect the stability of the phases promoting the formation of a PxOy phase.
Dissolution of PxOy could promote the formation of LaPO4 which will then react with the
sulfur and water.
An estimation of the possible reactions was derived from the use of lanthanum in
flue gas desulphurization and oxygen storage for automotive catalysts in exhaust
conversion. Each system uses a form of lanthanum derived from lanthanum oxide. The
lanthanum oxide is then hydrated and reacted with a form of sulfur.
Derivatives of this material can be formed through the following reaction.
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2La(OH)3 ↔ La2O3 + 3H2O
This reaction will occur naturally in lanthanum oxide powders exposed to the
atmosphere. The hydration / dehydration ranges are illustrated below.
2La(OH)3 � 2LaOOH � La2O3 377°C (-2H2O) 527°C(-H2O)
La(OH)3 readily transforms into La2O2S upon reaction with sulfur-bearing species, such
as SO2.
2La(OH)3 + SO2 ↔ La2O2S + 3H2O + 3/2O2
A novel method of oxygen storage utilizes lanthanum oxysulfate (La2O2SO4). This
material will produce free oxygen through the following reversible reaction:
La2O2SO4 ↔ La2O2S + 2O2
This is based on the redox of sulfur in a lanthanum oxysulfate / oxysulfide (La2O2SO4 /
La2O2S) system. The redox reaction is based on the S6+ and S
2- cycle [62-64]. The
resulting lanthanum oxysulfate/sulfide is the final product that eventually disintegrates
into the powder found on the bottom of the beaker.
In the present case, the corrosion process started with LaPO4 dissolving in a
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similar manner as phosphate glass and in the presence of other lanthanum compounds,
the system proceeds to the redox state. The impurities and non-stoichiometric species
greatly increase the negative influences of the acid. Dissolution of the grain boundary
increases the contact of the acid with the ceramic, increasing thereby the rate of
degradation. This proposed mechanism agrees well with the EDS analysis and the high
concentration of La, S, and O.
For further testing and defining the corrosion mechanism the suggested method is
outlined in the appendix A-4.
4.3.2 Hastelloy C22
Hastelloy C22 has better corrosion resistance compared to many other commercial
alloys. However, it does experience some corrosion and does not provide an adequate
lifetime for nozzles used in acid injection. The intention of using it in the current study
was to evaluate LaPO4 ceramic against the Hastelloy C22 for potential use as a nozzle.
In the process of comparison, the test protocol provided sufficient data to suggest a
plausible mode of corrosion and potentially identify corrective measures to improve the
material resistance.
Much consideration has thus far been put into the alloy composition, but little has
gone into how the acid interacts with it. The anodic passivity formed between the acid
and alloy involves the solid-state formation of a chromium-rich oxide–hydroxide passive
film with the participation of undissociated H2SO4 as the source of oxygen [65]. The
surface process of passivation has a strong build up of bisulfate/sulfate (HSO4-/SO4
2-) as a
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monolayer coverage. A significant part of the sorbed bisulfate/sulfate ions is strongly
bonded to the passive layer thus formed [66]. The SO42- bonds not only to the surface of
an oxide film formed during corrosion of the alloy sample, but are also incorporated into
the layer up to a depth of several monolayers [66, 67]. Bisulfite ions (even in low
concentration) inhibit the formation of the compact and protective passive layer and
increase the rate of alloy surface passivation (formation of a thicker surface layer) [67].
This can be seen in the tested samples of Hastelloy C22. The samples boiled in
the 99 wt % sulfuric acid did not experience advanced corrosion as did the samples
boiled in the 90 wt % sulfuric acid. This becomes evident while comparing the
microscopic features of the surface. The coupons exposed to the 99 wt % acid show a
high concentration of iron, sulfur and oxygen and have a black burnt appearance. This is
assumed to be the passivation layer. In the case of coupons exposed to 90 wt %, the
passivation layer appear gray and has same level of iron, sulfur and oxygen as the 99 wt
%, but also have increased chromium and nickel. The passivation layer was not uniform
on the 90 wt % and had shiny spots dispersed through the gray surface. Electron
microscopy of the shiny areas was found to have high concentration of iron,
molybdenum, nickel, chromium and oxygen. Nickel and molybdenum have much greater
presence than any other elements on the surface. It is assumed that these shiny areas
were located where penetration of the passivation layer had occurred. This is based on
the high concentrations of nickel and molybdenum signifying that the iron and chromium
had experienced advanced dissolution.
The SEM/EDS analysis was also used to further consider how the boiling acid
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was affecting the Hastelloy C22. For a mode of comparison a coupon of as-received non-
tested Hastelloy C22 was analyzed as shown below.
Figure 30. SEM/EDS analysis of as-received Hastelloy C22 [61]; two large peaks
are due to Fe and Ni.
The EDS microanalysis of the as-received Hastelloy C22 shows the high amounts
of the key alloying elements (iron, chromium, nickel and molybdenum). There is minimal
oxygen present, suggesting that only minimal oxidation occurred on the surface. A few
different locations were scanned which also showed very similar results.
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Figure 31. EDS Scans of Hastelloy C22 corrosion tested in 90 wt. % sulfuric acid.
Coupons exposed to acid had two levels of exposure, passivation and penetration.
The passivated layers had a uniformed black appearance and minimal weight loss; the
EDS patterns revealed mainly iron, sulfur and oxygen in the layer close to the surface.
Penetrated samples had a non-uniformed grayish appearance with random regions that
were shiny and metallic. EDS analysis of the gray areas revealed results similar to the
passivated layer, but the shiny areas were high in the alloying elements (iron, chromium,
nickel and molybdenum); no sulfur was present.
Passivation layers became more pronounced as acid strength decreased. All
samples exposed to the 99 wt. % H2SO4 had a corrosion rate two orders of magnitude
lower than those exposed to the 90 wt. % acid. All coupons had a black appearance
which is thought to be the passivation layer. EDS revealed that the major elements at the
surface were iron, sulfur and oxygen. It is assumed that the surface process of
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passivation has a strong build up of bisulfate/sulfate (HSO4-/SO4
2-) as monolayer
coverage. A significant part of the sorbed bisulfate/sulfate ions are strongly bonded to
the passive layers formed and the dominant element in the passive layer was iron. This
agrees with the corrosion mechanism being reaction limited by the mass transfer of iron
in stainless steel. The increased concentration of acid favored the alloy and limited
corrosion, whereas the lower concentration did not and iron was depleted at a much faster
rate.
This is supported by the rates of weight loss determined experimentally. The
presence of iron, chromium, nickel and molybdenum at the surface region show that the
iron concentration has decreased to a level that no longer supports a large buildup of
sulfates monolayer. It is not known as to why the 90 wt. % H2SO4 decreases the
effectiveness of the passivation layer. It is stipulated that the increased water content
increases the solubility of the passive compounds formed by the protective alloys and
increases the electrochemical potential for corrosion.
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Chapter 5
Conclusions and Recommendations
5.1 Conclusions
The sheer volume of sulfuric acid produced annually in the US as well as
globally, its diverse use and the inherent safety risks to people and the environment
require that robust and reliable processes are developed and implemented to mitigate the
risks associated with the spent/used acid disposal and the efficient production of fresh/
new batch. To improve the reliability of the process, the materials used to fabricate the
nozzles for the regeneration of spent sulfuric acid were analyzed in this thesis, with the
goal of increasing the corrosion resistance in the highly corrosive environment. The
material of specific interest was lanthanum phosphate monazite (LaPO4) due mainly to
many of its attractive physico-chemical attributes. Its performance was compared with
that of currently utilized material, viz., Hastelloy C22 as well as other alternative
substitutes that could potentially be used. While LaPO4 is known to exhibit exceptional
corrosion resistance in many applications under extreme and severe process conditions, it
did not show a corrosion resistance superior to that of the currently available materials for
sulfuric acid injection nozzles; hence, it cannot be considered a suitable replacement
material.
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LaPO4 was considered because of its reported chemical and thermal stability, in
addition to its easy machinability. To assess its compatibility as a nozzle material for
sulfuric acid injection into a thermal decomposition furnace, sintered coupons were
subjected to systematic tests and analyses, including the determination of its mechanical
properties, such as the coefficient of thermal expansion, phase transitions via
simultaneous thermogravimetry and differential scanning calorimetry. This determined if
the material could function as a bulk ceramic for composing a nozzle in the intended
temperature range.
With that done, it was further tested to assess its resistance to corrosive
environments. A series of boiling sulfuric acid tests with varying strengths was
conducted to quantify its resilience to aqueous acid corrosion. Field tests in a thermal
decomposition furnace examined how well the material performed in the high-
temperature corrosive process gas environment. Concurrently, other materials (Al2O3,
AISI 316, Hastelloy C22) were also subjected to identical tests. The results served as a
mode of comparison of the performance of LaPO4. Hastelloy C22 represented what was
currently in use, AISI 316 confirmed the requirement for specialty alloys and the two
ceramics (LaPO4 and Al2O3) explored future options of material design with LaPO4.
In the testing and analysis period, the LaPO4 synthesis protocol was also refined
to make the material behavior more in line with the required performance criterion. In
that aspect, it was found that using an organic binder (PVA) improved the densification
characteristics, which directly improved its resistance to degradation when subjected to
the boiling test in concentrated sulfuric acid. Improvements in the material synthesis of
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LaPO4 greatly improved its corrosion resistance, but the improvements were not
significant enough to establish LaPO4 as the material of choice for composing sulfuric
acid injection nozzles. LaPO4 experienced dissolution in sulfuric acid at a rate greater
than Hastelloy C22; Al2O3 on the other hand, exhibited superior resistance to the boiling
test compared to LaPO4 and Hastelloy C22 both.
5.2 Recommendations
The research conducted and reported here improved the understanding of how and
why the nozzles fail in this particular application of immense industrial application. One
of the key findings was the tendency for the pooled acid on the tip of the nozzles to
decrease in acid strength, which greatly increased the corrosion rate, due to the
hygroscopic properties of the acid and the high concentration of water in the combustion
process. The interaction between the nozzle and the corrosion process emphasized the
importance of future nozzles to utilizing geometries that minimize acid pooling on the tip
of the nozzle. Also, design consideration must be given to how the gun is inserted into
the furnace port. The gun must be installed in a manner that shields the nozzle from the
direct heat of the furnace and maximizes the drainage of pooled acid from the tip of the
nozzle. These discoveries are significant and are expected to improve future furnace
design and acid injection systems.
The superior corrosion resistance of Al2O3 system suggests that it should be used
to compose the nozzles, but the material is not machinable and does not fit into the
maintenance structure of the plant. However, based on the results obtained in this work
and the published research on the utilization of Al2O3 mixed with LaPO4 to form a
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composite could produce a machinable ceramic with improved toughness. It is suggested
that future research consider this composite for fabricating sulfuric acid injection nozzles.
The superior corrosion resistance exhibited by Al2O3 would provide a long, predictable
life for the nozzle, and the incorporation of the LaPO4 would increase the material
toughness and machinability, thus allowing it to be incorporated into the current
maintenance structure.
Not only was important information determined concerning the sulfuric acid
injection nozzles, but the details of material corrosion and concentrated sulfuric acid was
further defined. A better understanding of the mechanisms of corrosion in sulfuric acid
manufacturing were attained and can be used for future selection of materials and
alloying element concentrations for process equipment. The proposal that grain boundary
dissolution was the leading mode of failure for LaPO4 puts increased emphasis on
attaining ceramics of increased purity, reducing contaminants and minimizing side
reactions of lanthanum and phosphorous. Future research should consider the
relationship of sintering and microstructure to the corrosion resistance of LaPO4.
Optimization of the microstructure could reduce grain boundary dissolution and increase
corrosion resistance. The proposal about boundary dissolution also identifies the need to
improve the ceramic synthesis process and alloys with increased contents of
molybdenum, chromium and nickel. The study of injection nozzle corrosion will help
improve corrosion resistance materials in sulfuric acid manufacturing and illustrates the
need for more research in the field of corrosion.
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56. Romualdo R. Menezes, P.M.S., Ruth H.G.A. Kiminami, Microwave hybrid fast
sintering of porcelain bodies. Journal of Materials Processing Technology, 2007.
190: p. 223-229.
57. Apex Instruments, I. Method 3 Orsat Analyzer. 2002 [cited 2008 1-10-2008];
Available from: http://www.apexinst.com/products/orsat.htm.
58. Stephen Sung, G.S., Lyle F. Albright, Decomposition of Spent Alkylation Sulfuric
Acid to Produce Sulfur Dioxide and Water. Industrial Engineering Chemical
Research, 1993. 32: p. 2490-2494.
59. S. Lucas, E.C., D. Bernache-Assollant, G. Leroy, Rare earth phosphate powders
RePO4*nH2O (Re=La, Ce or Y) II. Thermal behavior. Journal of Solid State
Chemistry, 2004. 177: p. 1312-1320.
60. H.J. Grabke, D.M., E. M. Muller-Lorenz, A. Schneider, Role of sulphur in
carburization, carbide formation and metal dusting of iron. Surface and Interface
Analysis, 2002. 34: p. 369-374
61. Hare, E., SEM/EDS Analysis of Corrosion Test Samples. 2007, SEM Lab, Inc.:
Snohomish. p. 32.
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62. Machida, M.K., K.; Ito, K.; Ikeue, K., Large-Capacity Oxygen Storage by
Lanthanide Oxysulfate/Oxysulfide Systems. 2005. 17(6): p. 1487-1492.
63. Masato Machida, K.K., Kazuhiro Ito, Novel oxygen storage mechanism based on
redox of sulfur in lanthanum oxysulfate/oxysulfide. Chemical Communications,
2004. 2004(6): p. 662-662.
64. Jianxin Ma, M.F., Ngai Ting lau, Activation of La2O3 for the Catalytic Reduction
of SO2 by CO. Journal of Catalysis, 1996. 163(2): p. 271-278.
65. J.R. Kish, M.B.I., J.R. Rodda, Anodic behaviour of stainless steel S43000 in
concentrated solutions of sulphuric acid. Corrosion Science, 2003. 45: p. 1571-
1594.
66. D. Deb, S.R.I., V. M. Radhakrishnan, A comparative study of oxidation and hot
corrosion of a cast nickel base superalloy in different corrosive environments.
Materials Letters, 1996. 29: p. 19-23.
67. Christian Schmidt, K.R., Donald H. Bilderback, Rong Huang, In situ synchrotron-
radiation XRF study of REE phosphate dissolution in aqueous fluids to 800 °C.
Lithos, 2007. 95: p. 87-102.
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Appendix
A-1 Historical Industrial Corrosion Studies
The following tests were conducted on different feeds of spent sulfuric acid. The
test procedure was placing the specified material coupon in a beaker sealed from
atmosphere for the allotted time and measuring the weight change at the indicated times.
The same coupons were used for multiple times. The acid was maintained at room
temperature and the spent acid was as received from the refiner or petrochemical facility.
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67
Material Tested: A - 36
-0.6
-0.5
-0.4
-0.3
-0.2
-0.1
0
42 125 166
Time (hours)
Gra
ms
Spent A
Spent B
Spent C
Figure 32. A 36 mild steel tested in room temperature spent sulfuric acid.
Material Tested: SS 304
-0.0025
-0.002
-0.0015
-0.001
-0.0005
0
42 125 166
Time (hours)
Gra
ms
Spent A
Spent B
Spent C
Figure 33. AISI 304 tested in room temperature spent sulfuric acid.
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68
Material Tested: SS 316
-0.0018
-0.0016
-0.0014
-0.0012
-0.001
-0.0008
-0.0006
-0.0004
-0.0002
0
42 125 166
Time (hours)
Gra
ms
Spent A
Spent B
Spent C
Figure 34. AISI 316 tested in room temperature spent sulfuric acid.
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69
A-2 Corrosion Data
Table 7. Specific details of boiling acid corrosion tests on Hastelloy C22 Initial Final Difference
Coupon Mass (g) a b c t in2
cm2
Mass (g) Mass (g) Hours g / h g / cm2 g / cm2 / hr % Diff. % St.
0 19.0539 0.523 0.528 1.058 0.2555 1.0967 7.0757 19.0206 -0.0333 27.33 -0.001218 -0.00471 -0.000172202 -0.175 99
1 16.5078 0.525 0.532 0.925 0.2555 1.0332 6.6658 16.49505 -0.01275 29.67 -0.00043 -0.00191 -6.44747E-05 -0.077 99
2 16.9512 0.594 0.595 0.978 0.256 1.2385 7.9902 16.9116 -0.0396 45.55 -0.000869 -0.00496 -0.000108805 -0.234 99
3 15.6969 0.493 0.48 0.928 0.2555 0.9461 6.1036 15.6491 -0.0478 32.833 -0.001456 -0.00783 -0.000238519 -0.305 99
4 17.8088 0.529 0.53 0.93 0.2555 1.0427 6.7268 17.7816 -0.0272 45.417 -0.000599 -0.00404 -8.90315E-05 -0.152733 99
5 18.7335 0.496 0.495 1.079 0.255 1.0337 6.6688 18.6917 -0.0418 26.667 -0.001567 -0.00627 -0.00023505 -0.22313 99
6 15.71 0.508 0.488 0.93 0.2555 0.9799 6.3221 15.6495 -0.0605 25.5 -0.002373 -0.00957 -0.000375277 -0.385105 99
7 17.889 0.489 0.473 1.078 0.2565 1.0093 6.5116 17.8534 -0.0356 24.25 -0.001468 -0.00547 -0.000225451 -0.199005 99
8 16.3424 0.492 0.492 0.971 0.255 0.9707 6.2627 16.1996 -0.1428 122.25 -0.001168 -0.02280 -0.000186518 -0.873801 99
20 6.44 0.487 0.617 0.329 0.272 0.7256 4.6815 6.426 -0.014 69.33 -0.000202 -0.00299 -4.31344E-05 -0.217391 99
21 6.2164 0.315 0.331 0.568 0.271 0.4539 2.9285 6.2011 -0.0153 92 -0.000166 -0.00522 -5.67887E-05 -0.246123 99
22 10.411 0.49 0.496 0.6149 0.275 0.8138 5.2506
23 10.6404 0.446 0.469 0.658 0.274 0.7471 4.8197
24 8.6098 0.364 0.3805 0.646 0.272 0.5717 3.6881 7.6978 -0.912 47 -0.019404 -0.24728 -0.005261266 -10.59258 90
25 10.6318 0.4735 0.463 0.636 0.274 0.7799 5.0313
26 9.9289 0.463 0.469 0.5545 0.2725 0.7262 4.6853
27 11.3251 0.4575 0.465 0.7095 0.2747 0.7887 5.0883 11.2969 -0.0282 168 -0.000168 -0.00554 -3.2989E-05 -0.249004 99
28 14.4153 0.508 0.615 0.695 0.272 0.9418 6.0763
29 8.0466 0.3685 0.363 0.639 0.2725 0.5701 3.6779
211 8.8209 0.384 0.386 0.6545 0.272 0.6084 3.9255 8.3486 -0.4723 22.5 -0.020991 -0.12032 -0.005347423 -5.354329 90
INCHES Surface
Table 8. Specific details of boiling acid corrosion tests on LaPO4
(All final weights are zero)
Coupon Int. Wt. Final Wt. Wt. Loss Start Time Finish Time Total Time hours %ST
LaPO4 no Binder 3.5765 0 -3.5765 8/10/2007 18:30 8/11/2007 12:00 17.5 99
LaPO4 2% PVA 8/11/2007 14:15 8/16/2007 12:15 106.00 99
LaPO4 2% PVA 9/8/07 10:20 9/9/07 19:20 9 90 Microwave Sintered 1575'C
Microwave Sintered 1575'C
Microwave Sintered 1575'C
Table 9. Specific details of boiling acid corrosion tests on Al2O3 Coupon Int. Wt. Final Wt. Wt. Loss Time Hours g/hr % St.
1 5.1567 5.1652 0.0085 133.25 6.38E-05 99
2 5.0902 5.0536 -0.0366 73.41666667 -4.99E-04 90
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70
Table 10. Specific details of high temperature field tests of materials in the furnace
Material Initial Wt. Final Wt. Delta Wt. Duration (hours) Wt. / hour Temp Range Avg. Temp Comment
Al2O3 5.1091 5.3142 0.2051 504 4.07E-04 700 - 1800 850
Advanced Carburization built up on coupon from carbon steel dish. Coupon was still in original shape
and size, no visible damage.
LaPO4 (2%PVA) 1.3053 2.4806 1.1753 504 2.33E-03 700 - 1800 850
Advanced carburization built up on coupon from carbon steel dish. LaPO4 crumbled into pieces and
entire surface had carbon adhered onto it. No structural properties existed.
C22 14.4153 14.6343 0.219 504 4.35E-04 700 - 1800 850
Carburization occurred on the surface, the carburization from the carbon steel container did not
adhere. Can see carburization penetrated the C22 coupon to some extent. Wt. gain is a
combination of carburization of coupon and external sources of soot and carbon.
A36 Mild Steel 700 - 1800 850
The end cap used to hold the samples was corroded in half. It did not melt but turned into a charcoal
like substance with a large volume increase. This flakie substance (Carburization?) broke off
removing most of the metal. The whole cap was like this, losing the majority of its metal.
Al2O3 5.1798 5.1805 0.0007 64.5 1.09E-05 600 - 850 750
Appears the same as when put into the furnace no noticeable damage. Assume difference is within
error of scale. Assume Wt. change of 0.
LaPO4 (2%PVA) 0.4953 0.4962 0.0009 64.5 1.40E-05 600 - 850 750
Appears the same as when put into the furnace no noticeable damage. Assume difference is within
error of scale. Assume Wt. change of 0.
C22 9.9289 9.9309 0.002 64.5 3.10E-05 600 - 850 750
Exterior surface is extremely blackened and a black scale flaked off. Metal appears burned.
Assume wt. gain is due to carburization, if left in longer assume would be corroded further and start
to loose weight.
A36 Mild Steel 5.7901 5.6719 -0.1182 64.5 -1.83E-03 600 - 850 750
Exterior surface is extremely blackened and a black scale flaked off. Metal appears burned.
Assume wt. gain is due to carburization. This was the worst of all the materials.
304L 16.106 16.1013 -0.0047 64.5 -7.29E-05 600 - 850 750
Exterior surface is extremely blackened and a black scale flaked off. Metal appears burned.
Assume wt. gain is due to carburization.
Al2O3 5.1805 5.1822 0.0017 92.00 1.85E-05 850 - 1100 800
Appears the same as when put into the furnace no noticeable damage. Assume difference is within
error of scale. Assume Wt. change of 0.
LaPO4 (2%PVA) 0.4962 0.4965 0.0003 92.00 3.26E-06 850 - 1100 800
Appears the same as when put into the furnace no noticeable damage. Assume difference is within
error of scale. Assume Wt. change of 0.
C22 9.9309 9.9308 -1E-04 92.00 -1.09E-06 850 - 1100 800
Exterior surface is extremely blackened and a black scale flaked off. Metal appears burned.
Assume wt. gain is due to carburization, if left in longer assume would be corroded further and start
to loose weight.
A36 Mild Steel 5.6719 5.837 0.1651 92.00 1.79E-03 850 - 1100 800
Exterior surface is extremely blackened and a black scale flaked off. Metal appears burned.
Assume wt. gain is due to carburization. This was the worst of all the materials.
304L 16.1013 16.0448 -0.0565 92.00 -6.14E-04 850 - 1100 800
Exterior surface is extremely blackened and a black scale flaked off. Metal appears burned.
Assume wt. gain is due to carburization.
Al2O3 5.1822 5.1822 0 336 0.00E+00 850 - 1100 800 Appears the same as when put into the furnace no noticeable damage.
LaPO4 (2%PVA) 0.4965 0.4983 0.0018 336 5.36E-06 850 - 1100 800 Appears the same as when put inot the furnace no noticeable damage.
C22 9.9308 9.9321 0.0013 336 3.87E-06 850 - 1100 800 Blackened surface
A36 Mild Steel 5.837 6.2244 0.3874 336 1.15E-03 850 - 1100 800 Blackened surface, with a swollen outer layer that dusts off
304L 16.0448 16.0438 -0.001 336 -2.98E-06 850 - 1100 800 Blackened surface
These samples did not see a large change or carburization as did the previous samples. The
conditions seemed to track the lower rates of the furnace.
All Samples were placed in the furnace again after cooled, cleaned and weighed.
Samples below were held in a canister with a 1" hole facing the top of the duct, instead of an open tray.
All Samples were placed in the furnace again after cooled, cleaned and weighed.
AISI 316 High Temperature Acid
A series of tests were conducted on AISI 316 in the reflux unit. It was the original
intention to test the AISI 316 coupons as the other materials were tested in boiling
sulfuric acid. This did not occur. The heating element did not function properly and
heated the acid to just below boiling temperature. Since the acid was not boiling the tests
were not part of the controlled experiment and were not included with the results.
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71
Table 11. Corrosion information on the AISI 316 immersed in high temperature,
but not boiling 99 wt. % H2SO4
Initial Final Difference
Coupon Mass (g) a b c t in2
cm2
Mass (g) Mass (g) Hours g / h / cm2 % Diff.
3 8.1991 0.976 0.544 0.497 0.133 1.2756 8.2299 7.905 -0.2941 29.00 -1.23E-03 -3.586979 rolling boil
4 9.9541 1.005 0.6395 0.5671 0.13 1.4739 9.5092 9.9465 -0.0076 5.00 -1.60E-04 -0.07635 Simmer
5 6.9088 0.98 0.453 0.44 0.131 1.1319 7.3026 6.836 -0.0728 32.17 -3.10E-04 -1.053729 Simmer
6 8.4256 0.979 0.547 0.543 0.13 1.3217 8.5268 8.403 -0.0226 12.00 -2.21E-04 -0.26823 Simmer
INCHES Surface
-5.00E-04
-4.50E-04
-4.00E-04
-3.50E-04
-3.00E-04
-2.50E-04
-2.00E-04
-1.50E-04
-1.00E-04
-5.00E-05
0.00E+00
0.00 5.00 10.00 15.00 20.00 25.00 30.00 35.00
Time (HOURS)
WT
. L
oss
g/h
/cm
2
Figure 35. Corrosion rate of AISI 316 in high temperature 99 wt. % H2SO4.
The corrosion rates of the stainless steel 316 in high temperature concentrated
sulfuric acid are much greater than the rates of the Hastelloy by over two orders of
magnitude. Based on these results it was determined that further testing was not required.
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72
A-3 SEM/EDS
Samples to be Tested
Table 12. Details of coupons SEM/EDS analyzed
Material Condition State Test LaPO4 Purchased,
Calcined Virgin Powder SEM-EDS
LaPO4 Purchased,
Sintered Virgin Pellet SEM-EDS
LaPO4 (2% PVA)
synthesized, calcined Virgin Powder SEM-EDS
LaPO4 (2% PVA)
synthesized, Microwave
Sintered Virgin Pellet SEM-EDS
C22 Hastelloy As Received Coupon SEM-EDS
C22 Hastelloy
99% H2SO4 Boiled 24
hours Coupon SEM-EDS
C22 Hastelloy
99% H2SO4 Boiled 72
hours Coupon SEM-EDS
C22 Hastelloy
90% H2SO4 Boiled 24
hours Coupon SEM-EDS
C22 Hastelloy
90% H2SO4 Boiled 72
hours Coupon SEM-EDS
Methods of Analysis:
EDS:
This technique is used in conjunction with SEM and is not a surface science
technique. An electron beam strikes the surface of a conducting sample. The energy of
the beam is typically in the range 10-20keV. This causes X-rays to be emitted from the
contact point with the material. The energy of the X-rays emitted depends on the material
under examination. The X-rays are generated in a region about 2 microns in depth, and
thus EDS is not a surface science technique. By moving the electron beam across the
material an image of each element in the sample can be acquired in a manner similar to
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73
SAM. Due to the low X-ray intensity, images usually take a number of hours to acquire.
Elements of low atomic number are difficult to detect by EDS. The SiLi detector (see
below) is often protected by a Beryllium window. The absorption of the soft X-rays by
the Be precludes the detection of elements below an atomic number of 11 (Na). In
windowless systems, elements with as low atomic number as 4 (Be) have been detected,
but the problems involved get progressively worse as the atomic number is reduced.
SEM:
The scanning electron microscope (SEM) is a type of electron microscope capable of
producing high-resolution images of a sample surface. Due to the manner in which the
image is created, SEM images have a characteristic three-dimensional appearance and are
useful for judging the surface structure of the sample. Using the SEM the following
properties can be discovered.
• Fracture Surfaces
• Intergranular corrosion
• Grain surface
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74
Sample Preparation
The C-22 alloy is conductive and the coupons are small enough that they can be
test as is. The alloy will be tested for micro chemical analysis. The powders must be
single layered onto a carbon or copper tape so that during the EDS scan the powder is not
disrupted.
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A-4 Recommendations for Future Work
Lanthanum Phosphate
It was the intentions of this study to determine if lanthanum phosphate would be
an improved material for composing the sulfuric acid injection nozzles. Based on the
boiling acid test it was determined that the lanthanum phosphate as a bulk ceramic would
not be a good material for the task. The study did not conduct an in-depth analysis of
what was causing the material to degrade in the particular corrosive environment since it
was deemed unusable. Although the material did not work for this application it can be
applied to many useful purposes that do exhibit corrosive environments and an in-depth
study on the corrosion mechanism would be useful. The following outline suggests the
next steps in determining the cause of the corrosion in a highly acidic environment.
Analyze lanthanum phosphate ceramic samples that have been pressed and sintered as
follows.
• XRD - Surface and cross-sectional
• XRD – During a heat up and cool down
• SEM – Surface and cross-sectional
• EDS – Surface and cross-sectional
These tests should be conducted in a manner that allows the details of the bulk and
grain boundaries to be determined. The details of concern would be the structures,
phases, compositions, purities and interactions with each other.
Once this has been determined the samples can be exposed to the boiling acid tests
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76
for different exposure times. Reagent grade sulfuric acid and high purity water should be
used in volumes that would allow later analysis of the acid. This would determine what
is being dissolved in the acid. The sample in bulk and dissolved form should be
reclaimed. The reclaimed samples must be washed repeatedly with high purity water and
vacuum dried. The samples if not washed properly will absorb the moisture in the air and
excrete an acidic liquid.
Post analysis would be conducted as described in the pre-analysis. If the same
details are defined for the bulk and grain boundaries of the ceramic at the different
exposure times the mechanism for corrosion should be able to be determined. This
should assist in determining what is depleting the phosphate group and further
transformation to a La, O, and S composition.
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77
A-5 Alloy Composition
Table 13. Industrial utilized alloy compositions for nozzles
Alloy Ni Mo Fe Co Cr Mn Si C V W S Cu P Cb B2 69 28 2 1 1 1 0.1 0.01 0.0 0.0 0 0 0 0
C276 57 16 5 2.5 16 1 0.08 0.01 0.35 0.0 0 0 0 0
C22 56 13 3 2.5 22 0.5 0.08 0.01 0.35 3 0 0 0 0
Alloy 20 35 2.5 34.5 0 20 2 1 0.07 0 0 0.35 3.50 0.045 1
AISI304 8 0 71.3 0 17.5 2 1 0.08 0 0 0.03 0 0.045 0
AISI316 12 2.5 65.4 0 17 2 1 0.03 0 0 0.03 0 0.045 0
Alloy Comparison
0 10 20 30 40 50 60 70 80
Ni
Mo
Fe
Co
Cr
Mn
W
Cu
Ele
men
ts
Percent
SS316
SS304
Alloy 20
C-22
C-276
B-2
Figure 36. Element composition of the alloys considered.