Turbine Engine Abradable Systems

Abstract

In a method for forming an abradable material (36), the abradable material has at least 20% by volume rutile titania (44) and hBN (46). The method includes: blending a first titania powder having an oxygen debit of at least 5.0% with a second titania powder having an oxygen debit, if any, of less than 1.0%. The blend is thermal sprayed. The sprayed blend is then oxidized.

Claims

1. A turbine engine comprising: a first member having a surface bearing an abradable coating, the abradable coating being at least 90% by weight ceramic; and a second member having a surface bearing an abrasive coating, the abrasive coating comprising a metallic matrix and an ceramic oxide abrasive held by the metallic matrix, the first member and second member mounted for relative rotation with the abrasive coating facing or contacting the abradable coating, wherein: at least 50% by weight of the ceramic abrasive has a melting point at least 400K higher than a melting point of at least 20% by weight of the ceramic of the abradable coating.

2. The turbine engine of claim 1 wherein: the abradable coating has cohesive strength 800 psi to 3000 psi (5.5 MPa to 20.7 MPa).

3. The turbine engine of claim 1 wherein: the ceramic oxide abrasive forms at least 5% by weight of the abrasive coating.

4. The turbine engine of claim 1 wherein: at least 90% by weight of the ceramic oxide abrasive has a melting point at least 400K higher than a melting point of at least 20% by weight of the ceramic of the abradable coating.

5. The turbine engine of claim 1 wherein: at least 90% by weight of the ceramic oxide abrasive has a melting point 400K to 1850K higher than a melting point of at least 20% by weight of the ceramic of the abradable coating.

6. The turbine engine of claim 1 wherein: the abradable ceramic comprises a ceramic matrix and a ceramic filler; the ceramic filler is softer than the ceramic matrix; the ceramic filler has a melting temperature or a sublimation temperature higher than a melting point of said ceramic matrix; and/or the ceramic filler has a Mohs hardness 5.0 or less.

7. The turbine engine of claim 6 wherein: the ceramic filler is selected from the group consisting of: HBN; and Magnli phase titanium oxide.

8. The turbine engine of claim 1 wherein: the metallic matrix is an MCrAlY.

9. The turbine engine of claim 1 wherein: the first member comprises a blade outer airseal substrate having an inner diameter surface and a bondcoat atop the inner diameter surface, the abradable coating atop the bondcoat.

10. The turbine engine of claim 1 wherein: the at least 50% by weight of the ceramic oxide abrasive is selected from the group consisting of: zirconia, partially stabilized zirconia, chromia, and mixtures thereof; and/or the at least 20% by weight of the ceramic of the abradable coating is selected from the group consisting of: mullite.

11. The turbine engine of claim 1 wherein: the at least 50% by weight of the ceramic oxide abrasive is selected from the abrasives listed in Table I; and the at least 20% by weight of the ceramic of the abradable coating is selected from the abradables listed in Table I but meeting the identified Table I melting point and hardness criteria.

12. The turbine engine of claim 11 wherein: the abradable ceramic comprises a ceramic matrix and a ceramic filler; and the ceramic filler is listed in Table III as an abradable filer.

13. The turbine engine of claim 1 wherein: the at least 50% by weight of the ceramic oxide abrasive is 7YSZ; and the at least 20% by weight of the ceramic of the abradable coating is mullite.

14. The turbine engine of claim 1 wherein: the at least 50% by weight of the ceramic oxide abrasive is chromium oxide; and the at least 20% by weight of the ceramic of the abradable coating is rutile titania.

15. The turbine engine of claim 1 wherein: the at least 50% by weight of the ceramic oxide abrasive is zirconia-toughened alumina; and the at least 20% by weight of the ceramic of the abradable coating is enstatite.

16. The turbine engine of claim 1 wherein: the at least 50% by weight of the ceramic oxide abrasive is selected from the group consisting of: partially-stabilized zirconia; zirconia-toughened alumina; and chromium oxide; or the at least 50% by weight of the ceramic of the abradable coating is selected from the group consisting of: mullite; rutile titania; and enstatite.

17. A method for using the turbine engine of claim 1, the method comprising: running the engine to relatively rotate the first member and the second member; and the running causing the abrasive coating to contact and cut the abradable coating.

18. The method of claim 17 wherein: during the running, in absolute temperature, the local maximum operating temperature is at most 60% the melting point of at least 50% by weight of the ceramic of the abradable coating.

19. A method of coating a substrate with an abradable coating, the method comprising: blending powders and thermal spraying the blend; or co-thermal spraying, the co-thermal spraying forming a blend of the powders. wherein the blend comprises: at least 20% by volume mullite; and at least 35% by volume Magnli phase titanium oxide.

20. The method of claim 19 wherein: the blend further comprises a fugitive powder.

Description

BRIEF DESCRIPTION OF THE DRAWINGS

[0063] FIG. 1 is a schematic sectional view of a blade rub interaction in a gas turbine engine.

[0064] FIG. 1A is a micrograph of an abradable coating on one of two rubbing members in the interaction.

[0065] FIG. 1B is a four times further enlarged view of the micrograph of FIG. 1A.

[0066] Like reference numbers and designations in the various drawings indicate like elements.

DETAILED DESCRIPTION

[0067] Current abradable system pairs are a limiting factor for high pressure compressor (HPC) development. Further increasing compression in new engine designs involves increasing temperatures to the point of causing diffusion reaction and hot corrosion (particularly in the presence of environmental salts, most significantly such as when operating in coastal areas and/or desert areas (where dust-borne contaminants are an issue)). Sulfur compounds (e.g., sulfur dioxide, sulfates, sulfides, and the like) such as in polluted environments are also problems. In such conditions, it may be desirable to replace the baseline cBN with a more environmentally robust abrasive. Despite a high sublimation point of 3,246 K, cBN can suffer failures at lower temperatures. For example, conventional cBN abrasives operate well at temperatures in the range of 400 K to 900 K. At higher temperatures, (e.g., above 900K), oxidation starts to occur. Also, there can be reactions between the cBN and the matrix holding it (e.g., nickel or nickel alloy). At or above 1000 K, life will be very short.

[0068] FIG. 1 shows a turbomachine 20 first member 22 as a non-rotating shroud (e.g., segmented blade outer air seal (BOAS)) and second member 24 as a rotating blade. The first member 22 comprises a substrate 30 (e.g., metallic, such as nickel-based superalloy) having a surface 32. Along a portion of the surface 32 (e.g., a BOAS segment inner diameter (ID) surface in the example), the surface 32 bears a first coating system 34. The first system 34 includes an abradable coating (coating layer) 36 having an exposed surface 38. A bondcoat 40 (e.g., thermal sprayed MCrAlY or diffusion aluminide) may intervene between abradable coating 36 and the substrate 30.

[0069] The abradable coating 36 includes a ceramic 44 (FIG. 1A/1B) and optional filler 46 along with porosity 48. For ease of reference, the ceramic 44 will be referred to as a matrix or matrix phase even where there is no filler. In examples discussed below, the filler 46 is also ceramic (ceramic filler). The FIG. 1A/1B example is rutile titania ceramic 44 and hBN filler 46. In a thermal spray deposition of the abradable coating 36 the porosity will include a component merely due to the spray parameters and a component due to the inclusion of a fugitive powder (if any) in the spray feedstock. In use or in a pre-use heating, the fugitive is vaporized or decomposed to leave porosity. Example fugitives are polymers such as polyesters and/or acrylics (example fugitive content as applied is 10% to 20% by volume, more broadly 5.0% to 25.0%). Overall, the two-(or more)-component abradable may be 100% ceramic or an example at least 95% or at least 90% by weight (particularly after fugitive removal). Example by weight matrix content is at least 20% or at least 25% or at least 35% and may be as high as 75%.

[0070] The second member 24 comprises a substrate 50 (e.g., metallic, such as nickel-based superalloy) having a surface 52. Along a portion of the surface 52 (e.g., an airfoil tip surface in the example), the surface 52 bears a second coating system 54. The second system 54 includes an abrasive coating (coating layer) 56 having an exposed surface 58. A bondcoat 60 may intervene between abrasive coating 56 and the substrate. The presence and nature of a bondcoat 60 will be influenced by the nature and application technique of the matrix. The bondcoat may be an initial plating or strike of matrix material.

[0071] The abrasive coating 56 (FIG. 1) includes a metallic matrix 64 and a ceramic oxide abrasive 66 (replacing a baseline cBN) held by the matrix (e.g., as discrete particles within the matrix and optionally protruding at the surface 58. Example by weight abrasive content is at least 5% or at least 10%. Example upper limits for ranges using either of those lower limits are 60% or 50% or 40%. Broadly, the abrasive content may be effective from about 5v % to 80v % depending on application and method of manufacture, more narrowly 20v % to 70v %. The first member 22 and second member 24 are mounted for relative rotation about an axis 500 (engine centerline) with the abrasive coating facing or contacting the abradable coating.

[0072] In endeavoring to find a coating pair compatible with higher temperatures, there are competing considerations. Increasing the temperature capability of any given material potentially affects the performance of other materials. For example, it may increase the temperature-independent component of wear on other materials or it may exacerbate the temperature increase. For example, an increase in compression will thermodynamically correspondingly increase temperature at the last stage of the compressor. The increased material temperature capability may cause an increase in the operating temperature of the rub interface beyond that thermodynamic increase in local engine temperature.

[0073] We theorize that the material selections are bounded by two factors: the melting point of the abradable matrix 44 relative to the operating temperature (e.g., gas temperature measured via thermocouple); and the relative melting points of the abradable matrix 44 and abrasive particles 66.

[0074] Operating temperature should be no more than 80% (sintering occurring) of the abradable constituents' (matrix and filler) absolute melting point(s). More particularly, the operating temperature would be 75% or two thirds or less or 60% or less or 50% or less. This will reduce sintering and improve durability of the abradable coating. At 50% or less there should be essentially no sintering.

[0075] The abrasive melting point should be at least 400 Kelvin (K) greater than the abradable matrix melting point. When looking at multi-ceramic systems, this may be further defined. There may be multiple ceramic abrasives and all need not have this relation to the matrix. Similarly, in the abradable some ceramics, particularly the filler, may not have this relationship. Thus, this relationship may exist for an example at least 50% by weight (or at least 75% or at least 90% or at least 95% or 100%) of the ceramic abrasive and at least 20% by weight of the ceramic of the abradable (again with a full continuum of higher levels of 25% or further 5% increments up to 100%). When looking only at ceramic matrix, this relationship may exist for an example at least 50% by weight (or at least 75% or at least 90% or at least 95% or 100%) of the ceramic abrasive and at least 80% by weight of the ceramic matrix of the abradable (again with a full continuum of higher levels of 85% or further 5% increments up to 100% or at least 98%). Particular examples in the tables below highlight the relevance of these numbers.

[0076] Such melting point differences for material pairs are shown in Table I below. In addition to showing melting points, Table I also includes data reflecting the conventional requirement that the abrasive 66 is harder than the abradable matrix 44. The table shows Mohs data (nearest 0.5 Mohs) and reflects a minimum delta of 1.0 Mohs.

[0077] The abrasive will similarly be harder than the filler 46. Tables II and III show data with respective difference thresholds of 1.0 Mohs and 2.0 Mohs. In general, the filler will have a Mohs harness of less than 6.0 or less than 5.0.

[0078] These limitations provide for a stable abradable structure with time and temperature (low sintering of the abradable matrix) and effective cutting without excessive dulling of the abrasive. Relatively softer filler may be allowed to sinter (as it can still be cut) but not to melt.

[0079] The 400 K temperature margin relates to the softening induced by the flash temperature of asperity contact. The softening facilitates wear. Further refined melting temperature margin (delta) ranges between abrasive and abradable matrix may have upper limits influenced by the desired avoidance of abradable matrix sintering. Further refined ranges may have lower melting temperature margin limits of 500 K or 475 K or 450K. The larger the margin (melting temperature delta), the more desirable from a cutting perspective, however, the melting point margin is limited by the propensity to sinter as discussed above. An upper limit on margin is roughly open ended depending on materials and application environment. A general likelihood is that the margin will not be greater than 1850 K.

[0080] Given the options of additives and variations, the relative and absolute properties given above for the matrix phase 44, filler 46, their combination, and the abrasive 66 may be for 100% of such components or for at least 50% by weight, or at least 75% or at least 90% or at least 95%.

[0081] As secondary factors, the abradable coating 36 may be limited to 800 psi to 3000 psi (5.5 MPa to 20.7 MPa), more narrowly 1000 psi to 2000 psi (6.9 MPa to 13.8 MPa), cohesive strength to help facilitate good cutting response at high interaction rate. Cohesive strength may be measured by ASTM C633-13(2017), Standard Test Method for Adhesion or Cohesion Strength of Thermal Spray Coatings, ASTM International, West Conshohocken, Pennsylvania. Higher strength is associated with higher erosion resistance. However, higher strength is associated with damage to blades (or other rubbing parts) in a high interaction rate event, thus imposing an upper end on the desirable range. Also, abrasive matrix material, abradable coating porosity, and abradable coating soft filler content may come into play. Specifically, soft filler 46 may be incorporated into the abradable structure in a manner that reduces bonding between matrix particles in order to improve abradability while porosity and fugitive porosity formers may be used to enhance removal of matrix particles during rub interactions (for example by leaving space for particle deflection which leads to fracture wear mechanisms).

[0082] The abradable coating 36 will typically have between 20% and 50% of the matrix phase 44, by volume, depending on the material combinations, if any. The more structural contribution provided by the filler 46 (if present), the less matrix is required. There may be relevant relative properties of the matrix 44 and filler 46.

[0083] As a variation on pure hBN filler, the hBN filler may be bound by a binder such as bentonite. For example, 10%, by weight, bentonite (more broadly 5.0% to 15.0% or up to 25.0% for use in a low temperature ultimate operating environment (e.g., compressor sections which may operate at less than 1000 F. (538 C.) or less than 1500 F. (816 C.) v. turbine sections)) in a spray dried HBN agglomerate. Optionally that agglomerate can be heat treated to increase its strength. The agglomerate may then serve as spray feedstock. The bentonite may improve the economics of the spray process, making it more repeatable and improving the capture of HBN in the coating.

[0084] Magnli phase titanium oxide (as distinguished from rutile titania (TiO.sub.2)) is used in industry for its electrical properties. It may generally be represented by the formula Ti.sub.xO.sub.2x-1, where x is 4-9 (although some sources identify x as 4-10 or may identify it as TiO.sub.1.8). Magnli phase may have use in an abradable as filler. For example, an abradable coating 36 of mullite matrix 44 filled with Magnli phase titanium oxide filler 46 (e.g., Ex. 1 in Table IV below) may have an example composition of 25v % mullite, 50v % Magnli phase, 15% porosity formed from fugitive (e.g., polyester), and 10% inherent porosity from the deposition. An abradable coating made from rutile titania and incorporating only porosity (e.g., Ex. 2 in Table IV) to enhance abradability may be composed of 45v % titania, 10% inherent porosity and 45% porosity formed from fugitive (e.g., acrylic fugitive).

[0085] Magnli phase may also find use in the matrix, particularly in a blend. As discussed below, it may be desired to apply a ceramic that is deficient in oxygen (sub-stoichiometric). An as-sprayed coating (or phase within a coating layer) with an oxygen debit may be subject to oxidation (either in-use or in a pre-use heating in an oxidative environment (e.g., heat treating in an air furnace) or both). The oxidation will expand the phase. If there is an initial tensile stress, the oxidation will reduce the stress and potentially shift into a compressive stress regime. The fully oxidized structure will be that of rutile titania.

[0086] Use of this effect of oxidation may be desirable to solve issues of spallation or cracking of ceramic coatings due to tensile stresses. In an example thermal spray coating, the tensile stresses may come from thermally induced shrinkage during cooling after molten droplet deposition, mechanical stresses or CTE mismatch with the substrate when heated and the substrate has higher CTE than the coating. Reducing coating tensile stress (and/or increasing/imposing compressive stress) at ambient conditions relative to a baseline coating allow operation at higher temperatures before a threshold spallation-inducing tensile stress is reached.

[0087] Oxygen debit in an oxide of an element is measured relative to a fully oxidized element (true stoichiometric). TiO.sub.1.8 is nominally 10% oxygen deficient relative to the true stoichiometric TiO.sub.2. Thus blends of Magnli phase and TiO.sub.2 may yield coatings of oxygen debits up to about 10% (e.g., an example debit of 3.0% to 10.0%). An oxygen debit of 10% relative to true stoichiometric yields about 3% to 4% volumetric expansion upon full oxidation. Whereas TiO.sub.2 is generally regarded as having a maximum service temperature of about 1000 F. (538 C.), imposition of an ambient temperature compressive stress via inclusion of Magnli phase will increase this limit. Depending on content, the addition may increase this to about or above 1400 F. (760 C.), more narrowly in the range of 600 C. to 800 C. or 700 C. to 800 C.

[0088] Pure Magnli phase may be undesirable as a matrix for two reasons. Magnli phase has a low strength and low hardness which result in poor mechanical strength and wear resistance. Also, for pure Magnli phase in coating form the shift to compressive stress upon oxidation may be great enough to cause the coating to spall off of the substrate after oxidation. For example, after heat treatment or initial service, the coated part may return to a low temperature (e.g. ambient 21 C. or extreme cold conditions such as temperatures of 40 C. to 0 C.) whereupon the compressive stress increases sufficiently to spall. This might not occur in thin coatings of about 0.015 inch or less depending on the spray parameters used. Thus, a blend may offer sufficient hardness while limiting severe low temperature CTE mismatch problems and reducing high temperature CTE mismatch problems.

[0089] Thus, the Magnli phase may be an example 5% to 75% by volume of the as-sprayed matrix (thus by volume of the blend), more narrowly 5% to 50% or 5% to 25% for low Magnli or 20% to 50% for higher. Weight amounts may be similar. The expansion upon oxidation will be proportional based on that percentage to the approximately 3% to 4% noted above for the nominal Magnli phase material. With such Magnli blends, example combined porosity (or porosity former) and filler may be 25% to 50% by volume. This may be lower than other matrix compositions due to the relatively low fracture toughness of titania as compared with other matrix formers.

[0090] Further variations may involve a depth-wise gradient in the Magnli phase to TiO.sub.2 ratio. For example, the ratio may decrease from near the substrate to near the coating surface (e.g., so as to leave the region near the substrate or bond coat in a greater state of compression than the surface leading to improved thermal shock resistance which may be particularly important for a turbine air seal application where there is significant frictional heating during a rub event). Thus, although a pre-blend may be introduced to a single hopper/feeder, a blending feeder may draw from separate hoppers of the two.

[0091] Thus post-spray oxidation can be used to counteract both the residual tensile stress from a thermal spray deposition process and the additive CTE mismatch stresses that occur when ceramic coatings on metal substrates are used at elevated temperature.

[0092] While an abradable coating application is an example, the post-spray oxidation methods and mechanisms will be equally applicable to anti-friction coatings, anti-wear coatings, thermal barrier coatings, and environmental barrier coatings. Thus, these may lack additional abrasive of an abrasive coating or abradability-enhancing filler of an abradable coating.

[0093] While the foregoing example blend of oxygen-deficient ceramic and stoichiometric ceramic is of titanias, alternative materials could include: silica; silicates including rare earth silicates; alumina; chromia; hafnia; and partially or fully stabilized hafnia, zirconia, gadolinia and mixtures thereof. These combinations include one group where the stoichiometric material and oxygen-deficient material have the same base element (Ti in the first example) and other groups where different base elements may be used for the two.

[0094] One example of different base elements is forming zirconia toughened alumina by blending relatively oxygen-deficient zirconia with relatively stoichiometric alumina. This may be used in a wear-resistant coating such as used on clamping surfaces or as an anti-erosion coating in areas exposed to particulate impacts or on a smooth coating for a calendaring roll used in paper manufacture. The oxygen-deficient zirconia may be the minor fraction by weight and volume and the major fraction may be stoichiometric alumina. Although volume and weight fractions may be as above for the titania combinations, in further examples, the oxygen-deficient zirconia makes up from about 4 to 25 weight percent (more narrowly 5% to 15%) of the combination. In this example toughening is achieved in a thermal spray coating when the zirconia feed stock particles are smaller than the alumina particles, for example less than 50% (e.g., 25% to 50%) of the diameter (e.g., a D50 size) of the alumina when the materials have similar feed stock morphology (e.g., fused and crushed or otherwise solid. v. hollow).

[0095] The oxygen-deficient material (mixture) may be used as a layer (e.g., an environmental barrier layer) in a multilayer system such as an environmental barrier system (EBC). Non abradable system uses include other turbine engine components such as gaspath facing surfaces of blades, vanes, combustor panels and the like. When used in an application as barrier, as in an oxidation or corrosion barrier for example (e.g., atop an oxygen-scavenger layer (e.g., bondcoat layer such as having a metallic silicon contente.g., United States Patent Application Publication 20190119803A1, Tang; et al., published Apr. 25, 2019 and entitled Oxidation Resistant Bond Coat Layers, Processes for Coating Articles, and their Coated Articles, the disclosure of which is incorporated by reference herein in its entirety s if set forth at length) which is atop a ceramic (monolithic (e.g., silicon carbide)) or ceramic matrix composite (CMC) (e.g., silicon carbide composite such as SiC-SiC)), the volume expansion is beneficial to help counteract the shrinkage associated with sintering-caused closing of microcracks and pores. Such a layer may additionally or alternatively be used below an abradable layer. In the silicate example, the abradable layer could also be a silicate-based layer but with porosity in excess of that in the barrier layer (e.g., at least 5% porosity difference such as by adding at least 5% fugitive by volume (e.g., 5% to 25% or 10% to 20%) in the as-applied layer with a baseline porosity of the barrier layer (no fugitive or essentially none (e.g., less than 2%)) being in the vicinity of 2% to 15% or preferably 2% to 8% as applied but then decreasing to 2% or less after heat treatment)). For such silicate abradable layer, if formed using the same basic combination of the barrier layer, hBN filler may be added and bentonite may be added for coating systems at the lower end of a likely operating temperature range (e.g., up to 1200 C. in operation, thus omitting the bentonite for higher temperatures).

[0096] Further control over stress state may be achieved by controlling the extent of oxidation and temperature(s) at which it occurs during heat treatment in a controlled atmosphere. For example, an oxygen deficient silicate coating (e.g., from a blend of two silicates differing only in oxygen content) on a ceramic (e.g., silicon carbide) substrate may be sintered at a temperature of 2400 F. (1316 C.) for 4 hours with a controlled oxygen partial pressure in the atmosphere that is gradually raised (e.g., from 0.001 bar to 0.018 bar). An alternative substrate is a ceramic matrix composite (CMC, e.g., SiC-SiC). By doing this, the tensile stresses induced by sintering shrinkage may be counteracted to result in a lower flaw barrier layer that better protects the substrate from oxidation during service. An example is yttrium silicate Y.sub.2SiO.sub.5 and/or Y.sub.2Si.sub.2O.sub.7 in stoichiometric form as the first blend constituent and in oxygen-deficient form as the second. Generally, relative to the stoichiometric constituent, the oxygen-deficient constituent may be an example 5.0% to 20.0% oxygen deficient, more narrowly 5.0% to 15.0% or 7.0% to 12.0%.

[0097] In general, the oxygen-deficient constituent ceramic may be 5% to 75% by volume or weight of the combined oxygen-deficient constituent ceramic and the stoichiometric or less deficient constituent ceramic, more narrowly an alternative minimum is 10% and alternative maxima are 25% and 50%. The post-spray oxidation may be effective to reduce the net oxygen debit by at least 50%, more narrowly, at least 75% or 90%. In general, the less oxygen deficient constituent ceramic may have a debit of less than 1.0% or, more narrowly, up to 0.50%.

[0098] Bond coat composition is somewhat arbitrary when chosen from the MCrAlY group where M is Ni, Co or combinations thereof. An example composition is Ni 22Co 17Cr 12Al 0.5Hf 0.5Y 0.4Si (commercially available as Amdry 386-2 by Oerlikon Metco of Pfffikon Switzerland). The bond coat may be the limiting factor for max use temperature (measured at bond coat outer surface) in the vicinity of 1850 F or 2150 F (1283K or 1450K) when deposited by APS or HVOF respectively with the HVOF version being heat treated for 2 hrs at 1975 F (1352K) in vacuum and the APS not heat treated. Alternative application techniques include HVAF and wire spray methods. For non-MCrAlY bondcoats, (NiCr, NiCrAl, and the like) similar spray techniques may be used. The oxygen-deficient material may be applied directly to a part without bond coat alone or as a layer in a multilayer system such as an environmental barrier system (EBC).

[0099] The abrasive tip in an example is made by capturing the abrasive 66 in a matrix 64 of nickel-or cobalt-based alloy (e.g., plating such as electroplating; spray such as APS, HVAF, HVOF, and cold spray; and additive manufacturing processes such as laser fusing, brazing, and the like). The plating may contain alloying elements as either embedded particles, plating layers or may be co-deposited. An example composition is Ni22Cr6Al. More broadly, the abrasive matrix may also include MCrAlY as discussed for the bond coat for the abradable.

TABLE-US-00001 TABLE I Melting Temperature Difference between Abrasive and Abradable Matrix Abrasive Al.sub.2O.sub.3 Cr.sub.2O.sub.3 ZrO.sub.2 HfO.sub.2 Max Use Mohs Hardness Temp Mohs 9 8 8.5 6.5 Abradable Matrix Example (K) Hardness T.sub.melt (K), Delta 2323 2708 2950 3173 Al.sub.2O.sub.3 or zirconia-toughened 1549 9.0 2323 0* 385* 627* 850* Al.sub.2O.sub.3 ZrO.sub.2, with and without 1967 8.5 2950 627* 242* 0* 223* stabilization HfO.sub.2 2115 6.5 3173 850* 465* 223* 0* TiO.sub.2 (rutile) 1427 6.5 2140 183* 568 810 1033** La.sub.2Zr.sub.2O.sub.7 (pyrochlore) 1715 5.5 2573 250* 135* 377* 600 FeTiO.sub.3 (ilmenite) 882 5.5 1323 1000 1385 1627 1850 3Al.sub.2O.sub.32SiO.sub.2 (mullite) 1409 7.0 2113 210* 595 837 1060** Fe.sub.2SiO.sub.4 (fayalite) 1642 7.0 2463 140* 245* 487 710** CaSiO.sub.3 (wollastonite) 1209 5.0 1813 510 895 1137 1360 CaTiOSiO.sub.4 (titanite) 1105 5.5 1657 666 1051 1293 1516 Na.sub.3K(Al.sub.4Si.sub.4O.sub.16) (nepheline) 862 6.0 1293 1030 1415 1657 1880** MgSiO.sub.3 (enstatite) 1220 5.5 1830 493 878 1120 1343 *Fails T.sub.m criterion **Meets T.sub.m but fails hardness criterion Hardness criterion: Abradable matrix hardness 1 mohs point or more lower than matrix Temperature criterion: Melting temperature of abradable matrix 400 C. or more lower than abrasive

TABLE-US-00002 TABLE II Mohs Hardness, Delta Between Abradable Coating Filler and Matrix (One Point Threshold) Abradable Filler Ti.sub.xO.sub.2x1, where x CaF.sub.2 YPO.sub.4 Ca.sub.5(PO.sub.4).sub.3(OH) Cu.sub.2O is 4-9 (Magneli hBN (fluorite) (xenotime) (apatite) (cuprite) phases) Max Use Temp (K) 2164 1127 1512 1289 1003 1427 T.sub.melt (K) 3246 1690 2268 1933 1505 2140 Abradable Matrix Example T.sub.melt (K) Mohs Hardness, delta 2.0 4.0 4.5 5.0 3.75 3.0 Al.sub.2O.sub.3 or zirconia toughened 2323 9.0 7.0 5.0 4.5 4.0 5.25 6.0 Al.sub.2O.sub.3 ZrO.sub.2, with and without 2950 8.5 6.5 4.5 4.0 3.5 4.75 5.5 stabilization HfO.sub.2 3173 6.5 4.5 2.5 2 1.5 2.75 3.5 TiO.sub.2 (rutile) 2140 6.5 4.5 2.5 2 1.5 2.75 3.5 La.sub.2Zr.sub.2O.sub.7 (pyrochlore) 2573 5.5 3.5 1.5 1.0 0.5* 1.75 2.5 FeTiO.sub.3 (ilmenite) 1323 5.5 3.5 1.5 1.0 0.5* 1.75 2.5 3Al.sub.2O.sub.32SiO.sub.2 (mullite) 2113 7.0 5.0 3.0 2.5 2.0 3.25 4.0 Fe.sub.2SiO.sub.4 (fayalite) 2463 7.0 5.0 3.0 2.5 2.0 3.25 4.0 CaSiO.sub.3 (wollastonite) 1813 5.0 3.0 1.0 0.5* 0.0* 1.25 2.0 CaTiOSiO.sub.4 (titanite) 1657 5.5 3.5 1.5 1.0 0.5* 1.75 2.5 Na.sub.3K(Al.sub.4Si.sub.4O.sub.16) (nepheline) 1293 6.0 4.0 2.0 1.5 1.0 2.25 3.0 MgSiO.sub.3 (enstatite) 1830 5.5 3.5 1.5 1.0 0.5* 1.75 2.5 *Fails criterion Hardness criterion: Filler hardness 1 Mohs point or more lower than matrix Max use temperature = 0.667 T.sub.melt

TABLE-US-00003 TABLE III Mohs Hardness, Delta Between Abradable Coating Filler and Matrix (Two Point Threshold) Abradable Filler Ti.sub.xO.sub.2x1, where x CaF.sub.2 YPO.sub.4 Ca.sub.5(PO.sub.4).sub.3(OH) Cu.sub.2O is 4-9 (Magneli hBN (fluorite) (xenotime) (apatite) (cuprite) phases) Max Use Temp (K) 2164 1127 1512 1289 1003 1427 T.sub.melt (K) T.sub.melt 3246 1690 2268 1933 1505 2140 Abradable Matrix Example (K) Mohs Hardness, Delta 2.0 4.0 4.5 5.0 3.75 3.0 Al.sub.2O.sub.3 or zirconia-toughened 2323 9.0 7.0 5.0 4.5 4.0 5.25 6.0 Al.sub.2O.sub.3 ZrO.sub.2, with and without 2950 8.5 6.5 4.5 4.0 3.5 4.75 5.5 stabilization HfO.sub.2 3173 6.5 4.5 2.5 2.0 1.5* 2.75 3.5 TiO.sub.2 (rutile) 2140 6.5 4.5 2.5 2.0 1.5* 2.75 3.5 La.sub.2Zr.sub.2O.sub.7 (pyrochlore) 2573 5.5 3.5 1.5* 1.0* 0.5* 1.75* 2.5 FeTiO.sub.3 (ilmenite) 1323 5.5 3.5 1.5 1.0* 0.5* 1.75* 2.5 3Al.sub.2O.sub.32SiO.sub.2 (mullite) 2113 7.0 5.0 3.0 2.5 2.0 3.25 4.0 Fe.sub.2SiO.sub.4 (fayalite) 2463 7.0 5.0 3.0 2.5 2.0 3.25 4.0 CaSiO.sub.3 (wollastonite) 1813 5.0 3.0 1.0* 0.5* 0.0* 1.25* 2.0 CaTiOSiO.sub.4 (titanite) 1657 5.5 3.5 1.5* 1.0* 0.5* 1.75 2.5 Na.sub.3K(Al.sub.4Si.sub.4O.sub.16) (nepheline) 1293 6.0 4.0 2.0 1.5* 1.0* 2.25 3.0 MgSiO.sub.3 (enstatite) 1830 5.5 3.5 1.5* 1.0* 0.5* 1.75* 2.5 *Fails criterion Hardness criterion: Filler hardness 2 Mohs point or more lower than matrix Max use temperature = 0.667 T.sub.melt

TABLE-US-00004 TABLE IV Example Pairs Abrasive coating Abradable coating volume percentages volume percentages Matrix Abrasive Matrix Filler Ex. 1 Ni22Cr6Al partially stabilized zirconia (7YSZ) mullite Magnli phase 70 30 25 titanium oxide 50 Ex. 2 Ni22Cr6Al chromium oxide rutile titania none 80 20 45 Ex. 3 Ni22Cr6Al zirconia-toughened alumina (4 wt % zirconia) enstatite hBN 65 35 32 55 Ex. 4 Ni22Cr6Al zirconia (unstabilized, e.g., commercially pure) rutile titania hBN 80 20 35 55 Ex. 5 Ni phosphorus single crystal cubic boron nitride 25 Magnli-75TiO.sub.2 hBN 90 10 60 30 Ex. 6 Ni zirconia (unstabilized, e.g., commercially pure) 25 Magnli-75TiO.sub.2 none 70 30 65 Ex. 7 Ni22Cr6Al zirconia-toughened alumina (4 wt % zirconia) 10 Magnli-90TiO.sub.2 hBN bentonite 65 35 65 25 2.5 Ex. 8 Ni zirconia (unstabilized, e.g., commercially pure) 10 Magnli-90TiO.sub.2 hBN bentonite 70 30 65 25 2.5 Ex. 9 Ni phosphorus zirconia-toughened alumina (4 wt % zirconia) 10 Magnli-90TiO.sub.2 hBN bentonite 70 30 65 25 2.5 Ex. 10 Ni phosphorus zirconia (unstabilized, e.g., commercially pure) 10 Magnli-90TiO.sub.2 hBN bentonite 70 30 65 25 2.5 Ex. 11 Ni phosphorus zirconia-toughened alumina (4 wt % zirconia) rutile titania hBN bentonite 70 30 50 30 4.0 Ex. 12 Ni phosphorus zirconia (unstabilized, e.g., commercially pure) rutile titania hBN bentonite 70 30 45 40 4.0

[0100] In the examples above, the abrasive is fully dense. The abradable remainder in Table IV is porosity or fugitive porosity formers (to be volatilized or burned out in use).

[0101] Other situations in which the abradable material may be used include interfacing with knife edge seals. One area of such examples include knife edges on a shrouded blade. Another is knife edges on an ID platform of a vane interfacing with an abradable on a rotor spacer outer diameter.

[0102] The use of first, second, and the like in the following claims is for differentiation within the claim only and does not necessarily indicate relative or absolute importance or temporal order. Similarly, the identification in a claim of one element as first (or the like) does not preclude such first element from identifying an element that is referred to as second (or the like) in another claim or in the description.

[0103] Where a measure is given in English units followed by a parenthetical containing SI or other units, the parenthetical's units are a conversion and should not imply a degree of precision not found in the English units.

[0104] One or more embodiments have been described. Nevertheless, it will be understood that various modifications may be made. For example, when applied to an existing baseline configuration, details of such baseline may influence details of particular implementations. Accordingly, other embodiments are within the scope of the following claims.