Damper Seals and Hydrostatic Bearings for Pump Applications

Transcription

1 Design and Analysis of High Speed Pumps Damper Seals and Hydrostatic Bearings for Pump Applications Dr. Luis San Andres Mast-Childs Professor Presentation for lectures (a) and 1(b) Based on Lecture (3) delivered at Von Karman Institute Original March 006 (Nov 008, Nov 009) 1

2 Damper Seals & Hydrostatic Bearings LEARNING OBJECTIVES a) Physical mechanism for generation of direct stiffness in annular pressure seals & hydrostatic bearings. Select design conditions to obtain maimum (optimum) stiffness b) Bulk-flow equations for prediction of the flow and force coefficients in annular pressure seals and hydrostatic bearings c) Predictions for two water seals, long and short, for application as neck ring and interstage seals. Effect of seal length and inlet swirl on rotordynamic force coefficients d) Discussion on design of hydrostatic bearing for water pump and to replace oil-lubricated bearings. Effect of angled injection and considerations for improvements in stability margin

3 Annular Pressure Seals Radial seals (annular, labyrinth or honeycomb) separate regions of high pressure and low pressure and their principal function is to minimize the leakage (secondary flow); thus improving the overall efficiency of a rotating machine etracting or delivering power to a fluid. Inter-stage seal Impeller eye or neck ring seal Balance piston seal Figure 1 Seals in a Multistage Centrifugal Pump or Compressor 3

4 Annular Pressure Seals Non-contacting fluid seals are leakage control devices minimizing secondary flows in turbomachines. Seals use process liquids of light viscosity as the working fluid. The dynamic force response of pressure seals has a primary influence on the stability response of high-performance turbomachinery. Annular seals, although geometrically similar to plain journal bearings, show a flow structure dominated by turbulence and fluid inertia effects. Operating characteristics unique to seals are the * large aial pressure gradients, * large clearance to radius ratio (R/c) < 500, while * the aial development of the circumferential velocity determines the magnitude of cross-coupled (hydrodynamic) forces. 4

5 Annular Pressure Seals Due to their relative position within a rotor-bearing system, seals modify sensibly the system dynamic behavior. Seals typically "see" large amplitude rotor motions. This is particularly important in back-to-back compressors and long-fleible multiple stage pumps. Figure 1 Straight-Through and Back-to-back Compressors and 1st Mode Shapes 5

6 Annular Pressure Seals Figure 3 Intentionally roughened stator surfaces (macro teturing) reduce the impact of undesirable cross-coupled dynamic forces and improve seal stability. These seals are common practice in current damper seal technology for cryogenic turbo pumps. Annular seals acting as Lomakin bearings have potential as support elements (damping bearings) in high speed cryogenic turbo pumps as well in process fluid applications. Honeycomb and round hole pattern seals for turbopump 6

7 Annular Pressure Seals The Lomakin Effect: generation of support (direct) stiffness L Aial velocity, V z shaft c D P s Aial velocity, V z c P a Process P s fluid at high Ps P a P e L Eit pressure P a z 4: Geometry of an annular pressure seal 5: Inertial pressure drop due to a sudden contraction The direct stiffness is due to the pressure drop at the seal inlet plane and its close interaction with the pressure drop (and flow resistance) within the seal lands (even without shaft rotation). The entrance effect is solely due to fluid inertia accelerating the fluid from the upstream (stagnant) pressure supply to a flow with a high aial speed and reduced static pressure. Figures 4 & 5 7

8 Annular Pressure Seals Force - P supply C V z eccentricity Inlet pressure drop Bernoulli equation: P+ρ (1+ζ)V z /=const. continuity equation: ρv z c=const. + C V z c V z P P inlet + P inlet (1+ξ) ρv z / (1+ξ)ρV z / μ κ V z L / C Ω c V z P - The Lomakin force (restoring force effect) P eit 8

9 Annular Pressure Seals K = B L c o K ( P P ) s a Optimum stiffness * Typical design condition pressure drop at inlet Too large clearance Or short seal pe: pressure ratio (entrance/supply) pressure drop in land Too tight clearance Or Long seal Seal wear enlarges clearance and increases leakage Figure 6 Stiffness versus entrance pressure ratio (simple model) 9

10 Force Coefficients in Annular Seals D D c P e P s rotor L L stator Depiction of an annular pressure seal P a Ω V z Aial velocity Aial pressure field Ω Y Seal reaction forces are functions of the fluid properties, flow regime, operating conditions and geometry. For small amplitudes of rotor lateral motion: forces represented with linearized stiffness, damping and inertia force coefficients: - F F y K = K y K K y yy C Y + C y C C y yy M + Y M y M M y yy Y 10

11 11 Force/Moment Coefficients in Seals Seals also generate moment coefficients due to tilts (angulations) of rotor. Most complete model: 16 stiffness, 16 damping and 16 inertia coefficients Y Z Y Seal with dynamic translations (,Y) and angulations (, Y) Δ Δ Δ Δ Δ Δ Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y Y e e M M M M M M M M M M M M M M M M - e e C C C C C C C C C C C C C C C C - e e K K K K - K K K K K K K K K K K K = - M M F F Figure 7

12 1 Bulk-flow Analysis of Annular Pressure Seals ( ) ( ) 0 = + + t h hv z hv z = z V V V t V h U V h P h z J ρ κ κ μ = z V V V t V h V h z P h z z z z z ρ κ μ Flow Continuity Circumferential Momentum transport Aial momentum transport Pa - Turbulent flow with fluid inertia effects - Mean flow velocities average across film (h) - No accounting for strong recirculation zones z Vz Ω Ps V

13 Bulk-flow Analysis of Annular Pressure Seals Boundary Conditions -Inlet pressure loss due to fluid inertia (Lomakin effect) - Inlet swirl determined by upstream condition (implementation of swirl-brakes) -Eit pressure without recovery loss, typically P e 1 = Ps - ρ (1+ ξ) V z, V = α Ω R Numerical Solution -Analytical solutions for short length seals (centered condition) See Childs tetbook -Numerical solutions for realistic geometries use CFD techniques (staggered grids, upwinding, etc) and predict (4 or 16) K,C,M force/moment coefficients. Radial baffles retarding fluid swirl Fluid path Ps Seal z Vz V Rotor speed rotor Ω Figure 8 Anti swirl brake at inlet or pressure seal 13

14 Dynamic Performance of Annular Seals Eample: (centered seal) Fluid: water at 30 C ( 0.79 cpoise, 995 kg/m3) Centered seal (e=0): No static load D = mm (6 inch), Short seal (neck ring seal) L/D=0.0 Long seal (inter stage seal) L/D= 0.50 c = mm, nominal clearance & worn clearance (c) smooth rotor and stator surfaces Nominal speed = 3600 rpm, Pressure drop 34.4 bar neck ring seal & inter stage seal or balance piston Standard design practice: find influence of seal wear on leakage and rotordynamic coefficients Pressure drop ΔP ~ RPM Inlet loss coefficient ξ=0.1 Inlet swirl α=0.5 and 0.0 (without and with swirl break) Influence on cross-coupled stiffness and stability Table 1 Geometry and operating conditions of water seals in a liquid pump 14

15 Entrance pressure into seal LONG SEAL SHORT SEAL Pressures vs shaft speed bar water seal, L/D=0.50, c=0.190 mm, D=15 mm No effect of inlet swirl on entrance pressure operating speed 3600 rpm Pressures vs shaft speed bar water seal, L/D=0.0, c=0.190 mm, D=15 mm No effect of inlet swirl on entrance pressure operating speed 3600 rpm 50 Ps 50 Supply pressure c c Supply pressure c c 10 Supply pressure Nominal clearance (C) Twice clearance (worn) 10 Supply pressure Nominal clearance (C) Twice clearance (worn) Rotor Speed (RPM) RPM L/D= Rotor Speed (RPM) RPM L/D=0.0 - Worn seal leads to lower entrance pressure loss due to increase in flow rate (reduction in land flow resistance) - Short seal leads has lowest entrance pressure due to increase in leakage Figure 9 Supply and entrance pressures for two water seals, L/D=0.50 and 0.0, and two clearances (c and c) 15

16 Entrance pressure ratio into seal LONG SEAL SHORT SEAL Inlet Pressure vs shaft speed c water seal, L/D=0.50, c=0.190 mm, D=15 mm No effect of inlet swirl on entrance pressure operating speed 3600 rpm Inlet Pressure vs shaft speed c water seal, L/D=0.50, c=0.190 mm, D=15 mm No effect of inlet swirl on entrance pressure operating speed 3600 rpm Entrance pressure ratio c Entrance pressure ratio c (Pe-Pa)/(Ps-Pa) Rotor Speed (RPM) RPM nominal C, swirl=0.5 nominal C, swirl=0.0 Twice clearance (worn) swirl=0.5 L/D= (Pe-Pa)/(Ps-Pa) Rotor Speed (RPM) RPM nominal C, swirl=0.5 nominal C, swirl=0.0 Twice clearance (worn) swirl=0.5 L/D=0.0 - Worn seal leads to higher entrance pressure loss due to increase in flow rate (reduction in land flow resistance) - Short seal leads to even larger inlet pressure loss due to increase in leakage Figure 9 Entrance pressure ratio for two water seals and two clearances (c and c) 16

17 Seal Leakage LONG SEAL SHORT SEAL Leakage vs shaft speed kg/s Nominal condition water seal, L/D=0.50, c=0.190 mm, D=15 mm No effect of inlet swirl operating speed 3600 rpm Leakage vs shaft speed kg/s water seal, L/D=0.0, c=0.190 mm, D=15 mm No effect of inlet swirl operating speed 3600 rpm Flow rate 10 8 c Flow rate 10 8 c c Nominal clearance (C) Twice clearance (worn) 4 c Nominal clearance (C) Twice clearance (worn) Rotor Speed (RPM) RPM & Psupply L/D= Rotor Speed (RPM) RPM L/D=0.0 - Leakage is proportional to RPM ~ ΔP & not proportional to clearance - Worn seal leaks more Longer seal leaks less - No influence of inlet swirl 1/ Figure 10 Leakage (flow rate) for two water seals, L/D=0.50 & 0.0, and two clearances 17

18 Drag Power LONG SEAL SHORT SEAL 6 Power vs shaft speed kw Nominal condition water seal, L/D=0.50, c=0.190 mm, D=15 mm minor effect of inlet swirl operating speed 3600 rpm 6 Power vs shaft speed kw water seal, L/D=0.0, c=0.190 mm, D=15 mm minor effect of inlet swirl operating speed 3600 rpm Drag Power 3 c c Drag Power 3 1 Nominal clearance (C) Twice clearance (worn) "" no swirl 1 c c Nominal clearance (C) Twice clearance (worn) "" no swirl Rotor Speed (RPM) RPM & Psupply L/D= Rotor Speed (RPM) RPM L/D=0.0 - Drag Power ~ RPM - Long seal draws more power (~ 5 times) - No effect of clearance. As C increases, so does circ. Reynolds # - No effect of inlet swirl Figure 11 Drag Power for two water seals, L/D=0.50 & 0.0, and two clearances 18

19 Rotordynamic coefficients lateral motions Seal reaction forces: - F F y K = K y K K y yy C Y + C y C C y yy M + Y M y M M y yy Y Reduced model: K = KYY, KY = -KY C = CYY, CY = -CY M = MYY, MY = -MY KY Whirl frequency ratio WFR ~ C Ω Assumes: No static load capability Circular centered orbit : measure of rotordynamic stability Y Rotordynamic Coefficients Centered Condition 19

20 Seal direct stiffnesses LONG SEAL SHORT SEAL Direct Stiffness vs shaft speed K=Kyy [MN/m] Nominal condition water seal, L/D=0.50, c=0.190 mm, D=15 mm negligible effect of inlet swirl operating speed 3600 rpm Direct Stiffness vs shaft speed K=Kyy [MN/m] water seal, L/D=0.0, c=0.190 mm, D=15 mm negligible effect of inlet swirl operating speed 3600 rpm Stiffness c c Stiffness c c Rotor Speed (RPM) Nominal clearance (C) Twice clearance (worn) ""no swirl RPM & Psupply L/D= Rotor Speed (RPM) RPM Nominal clearance (C) Twice clearance (worn) ""no swirl L/D=0.0 - Direct stiffness ~ Pressure supply ~ RPM - Long seal has ~ larger stiffness than short seal - Worn clearance causes ~ 50% drop in direct stiffness. It will affect pump WET natural frequencies - No effect of inlet swirl 1/ Figure 1 Direct stiffnesses K=KYY for two water L/D seals & two clearances 0

21 Seal direct stiffnesses Dim Direct Stiffness vs pressure ratio K=Kyy [-] water seal, L/D=0.50, 0.0, c=0.190 mm, D=15 mm negligible effect of inlet swirl c k = K c K c k = ( P s Pa ) L D ( P s Pa ) 0.35 L/D=0.5 L/D=0.5, c Stiffness L/D=0.5, c, a=0.5 L/D=0.5, c, a=0.0 L/D=0.5, c, a=0.5 L/D=0.5, c, a=0.0 L/D=0., c, a=0.5 L/D=0., c, a=0.0 L/D=0., c, a=0.5 L/D=0., c, a=0.0 Simple formula L/D=0. L/D=0., c L/D=0., c c L/D=0.5, c RPM increases Entrance Pressure ratio - Direct stiffness follows simple formula L/D=0.50, 0.0 Figure Dimensionless stiffnesses K=KYY for two water L/D seals & two clearances 1

22 Seal cross-coupled stiffnesses LONG SEAL SHORT SEAL Cross Stiffness vs shaft speed Ky=-Ky [MN/m] Nominal condition water seal, L/D=0.50, c=0.190 mm, D=15 mm large effect of inlet swirl operating speed 3600 rpm 1C Cross Different Stiffness scale vs shaft speed Ky=-Ky [MN/m] water seal, L/D=0.0, c=0.190 mm, D=15 mm large effect of inlet swirl operating speed 3600 rpm 1C Stiffness Nominal clearance (with swirl) "" no swirl Twice clearance (worn) "" no swirl c c 50% inlet swirl C Stiffness Nominal clearance (with swirl) "" no swirl Twice clearance (worn) "" no swirl c c 50% inlet swirl C 15.0 no inlet swirl Inlet swirl =0 10 no inlet swirl Rotor Speed (RPM) L/D=0.50 Rotor Speed (RPM) RPM & Psupply RPM L/D=0.0 - Cross stiffness ~ RPM & 1/clearance - Long seal has ~ 5 more cross-stiffness than short seal - Worn clearance drop in cross-stiffness. - Inlet swirl ~ 0 has most pronounced effect (KY <0 favors stability) Figure 13 Cross stiffnesses KY=-KY for two water L/D seals and two clearances

23 Seal direct damping coefficients LONG SEAL SHORT SEAL Damping Damping vs shaft speed C=Cyy Cy=-Cy [kns/m] C Nominal clearance (with swirl) Cy C Twice clearance (worn) Cy Nominal condition c little effect of inlet swirl c water seal, L/D=0.50, c=0.190 mm, D=15 mm operating speed 3600 rpm C 50% inlet swirl 1C C Damping Different Damping scale vs shaft speed C=Cyy Cy=-Cy [kns/m] C Nominal clearance (with swirl) Cy C Twice clearance (worn) Cy water seal, L/D=0.0, c=0.190 mm, D=15 mm little effect of inlet swirl operating speed 3600 rpm c c 1C 50% inlet swirl C C 40 0 Cy 10 5 Cy Rotor Speed (RPM) RPM & Psupply L/D= Rotor Speed (RPM) RPM L/D=0.0 - Direct damping ~ effective turbulent flow viscosity & 1/clearance - Long seal has ~ 5 more direct damping than short seal - Worn clearance drop in damping - Inlet swirl no effect. C >> CY Figure 14 Damping C=CYY & CY=-CY for two L/D water seals and two clearances 3

24 Seal added mass or fluid inertia coefficients LONG SEAL SHORT SEAL Direct Inertia vs shaft speed c water seal, L/D=0.50, c=0.190 mm, D=15 mm negligible effect of inlet swirl operating speed 3600 rpm Direct Different Inertia scale vs shaft speed M=Myy [kg] Nominal condition water seal, L/D=0.0, c=0.190 mm, D=15 mm negligible effect of inlet swirl operating speed 3600 rpm Nominal clearance (C) Twice clearance (worn) ""no swirl Added mass c Added mass c M=Myy [kg] Nominal clearance (C) Twice clearance (worn) ""no swirl c Rotor Speed (RPM) RPM & Psupply L/D= Rotor Speed (RPM) RPM L/D=0.0 - Direct inertia invariant with speed & proportional to 1/clearance - Long seal has ~ 0 more added mass than short seal - Worn clearance drop in added mass - Inlet swirl no effect. M >> MY - Large inertia will affect wet pump critical speeds Figure 15 Inertia M=MYY for two L/D water seals and two clearances 4

25 Fluid inertia Its magnitude M fluid := ρπ D L c M steel := ρ steel π M := ρπ D 3 L 1 c tanh L D L D D L D=15.4 mm c =0.190 mm μ=0.79 cpoise ρ=995 kg/m3 LONG SEAL L/D=0.5 SHORT SEAL L/D= M = 4.03kg M fluid = kg M = 3.88 M steel M steel = 10.84kg 0. M =.91kg M fluid = kg M = 0.67 M steel M steel = 4.34kg -Fluid mass inside film is just a few grams, but. since added mass is proportional to Diameter and 1/clearance M can be larger than mass of solid steel of same dimensions FLUID INERTIA How large is it? 5

26 Whirl frequency ratio Stability indicator Whirl frequency ratio LONG SEAL Whirl ratio vs shaft speed WFR c c c Nominal clearance (with swirl) "" no swirl Twice clearance (worn) "" no swirl water seal, L/D=0.50, c=0.190 mm, D=15 mm large effect of inlet swirl operating speed 3600 rpm 50% inlet swirl 1C no inlet swirl Whirl frequency ratio Inlet swirl =0 SHORT SEAL Whirl ratio vs shaft speed WFR Nominal condition Nominal clearance (with swirl) "" no swirl Twice clearance (worn) "" no swirl water seal, L/D=0.0, c=0.190 mm, D=15 mm large effect of inlet swirl operating speed 3600 rpm 50% inlet swirl no inlet swirl c C 0.1 negative values C 1C Rotor Speed (RPM) L/D= Rotor Speed (RPM) L/D=0.0 RPM & Psupply RPM - WFR always 0.50 for inlet swirl = 0.50 Stable up to critical speed - Inlet swirl = 0.0 drops WFR, in particular for short seal. - Inlet swirl =0.0 does not help greatly in long seal with tight clearance Figure 16 Whirl frequency ratio for two L/D water seals & two clearances 6

27 Tetured Surface Annular Seals Hole-Pattern Seal Unwrap Honeycomb Seal Unwrap -Machined roughness in seal surfaces aids to increase friction thus reducing leakage. - Surface teturing also reduces development of mean circumferential flow velocity, thus decreasing cross-stiffnesses. -Proven improvement in stability margins in pumps and compressors -Teturing works only on stationary surface. Opposite rotordynamic effect if rotor is rough. 7

28 Hole pattern seal in compressors Hole damper seal replacing labyrinth seal in division wall of back-to-back compressor 005 Turbomachinery Symposium 8

29 Hole pattern seal INSTABILITY Waterfalls before (with original labyrinth seals) and after installation of hole-pattern seal in division wall - 9

30 Hydrostatic Bearings for pump applications Eternal pressure source forces fluid to flow between two surfaces, thus enabling their separation and the ability to support a load without contact. Advantages Support very large loads. The load support is a function of the pressure drop across the bearing and the area of fluid pressure action. Load does not depend on film thickness or lubricant viscosity Long life (infinite in theory) without wear of surfaces Provide stiffness and damping coefficients of very large magnitude. Ecellent for eact positioning and control. Disadvantages Require ancillary equipment. Larger installation and maintenance costs. Need of fluid filtration equipment. Loss of performance with fluid contamination. High power consumption: pumping losses. Limited LOAD CAPACITY ~ f(psupply) Potential to induce hydrodynamic instability in hybrid mode operation. Potential to show pneumatic hammer instability with compressible fluids 30

31 Hydrostatic Bearings for turbopumps Low cost primary power cryogenic turbo-pumps (TP) are compact, operate at high speeds, and require of eternally pressurized fluid film bearings to support radial and thrust loads. Hybrid thrust & radial bearings enable smaller and lighter turbopumps with no DN life limitations Large stiffness (accuracy of positioning) and damping force coefficients allow for unshrouded impellers with increased TP efficiency 31

32 Support stiffness in a Hydrostatic Bearing P s Q r Feed restrictor Flow through restrictor = Flow through film lands P a L Film land P R, recess pressure b L Fluid flow, Ql Figure 18: Geometry of a simplified 1-D hydrostatic bearing P a h p h Q Q r r = Q = Q c o = = A C o d π d 4 18 μ c ρ ( P P ) s ( P P ) s R R orifice capillar P s Supply pressure P R, recess pressure Q = 3 ( P P ) B h P B h R = + 1μ 1 μ L 3 a Land flow P a Film land L Figure 19: Typical pressure drop in a hydrostatic bearing (laminar flow without fluid inertia effects, incompressible fluid) Figures 18 & 19 b L P a As film thickness decreases, resistance in land increases, thus reducing flow rate and increasing pressure in pocket or recess. Stiffness generated from changes in pocket pressure 3

33 Static support stiffness in a Hydrostatic Bearing 0.4 Dimensionless stiffness for simple HB Typical design condition K c Ps Area stiffness (dimensionless) 0. orifice capillar Figure 0: Static stiffness for simple hydrostatic bearing (laminar flow w/o fluid inertia effects, incompressible fluid). Figure ifi pocket pressur ratio (Pr/Ps) Low recess pressure Too large clearance Or too small orifice diameter High recess pressure drop Too tight clearance Or too large orifice No need of journal rotation Stiffness is proportional to supply pressure and bearing (pocket) area. Stiffness is inversely proportional to clearance Stiffness changes quickly with variations in pocket pressure Hydrostatic bearings have LIMIT load capacity 33

34 Traditional hydrostatic bearing design: * large pocket area (80-90 % of total area) * deep pocket depth * large orifice discharge volume Applications: low or null surface speed, low frequencies, nearly incompressible fluids (water or mineral oil) produces very large DIRECT Stiffness. Warning: This design should NEVER be used with compressible liquids or gases 34

35 Fluid Compressibility Effects Pneumatic Hammer is a self-ecited instability (loss of damping) in poorly designed hydrostatic bearings for applications with compressible liquid and gases. The instability arises due to trapped fluid volume in the bearing pockets generating a dynamic pressure that lags journal motions by ~ (+)90 degrees. Remedies to AVOID (reduce and even eliminate) pneumatic hammer are WELL KNOWN (documented analysis and operation verification) and can be implemented easily at the design stage. 35

36 Fluid compressibility Effects Low frequency Loss of damping if fluid is compressible Dimensionless stiffness and damping K/Ko C/Co Coefficients for hydrostatic bearing C K ecitation frequency/break frequency K f ( ω ) = ω ω = K B ( 1+ f ) High frequency Stiffness Hardening effect Complete loss of damping f α ; C ( ω ) = C 0 ( 1 α ) ( 1+ f ) Coefficients depend on BREAK frequency: ω = B ( Z + 1) κ V rec 0 3 h0 B 6 μ L A function of fluid bulk modulus (κ)/pocket volume Ko α = ω C B o Figure Frequency dependent force coefficients for simple hydrostatic bearing 36

37 Whirl frequency ratio of centered HJB φ = WFR = K ΩC Y f K Y = 0.5 ΩC 1 == 0 = 0 1 ( 1 α ) ( α ) Whirl frequency ratio Ko α = ω C B o ω B = Q P r R 0 ( Z + 1) V rec 0 κ = ( Z 1) 0 + κ V rec 0 3 h0 B 6μ L WFR in a hydrostatic bearing can be WORSE than that of a plain journal bearing due to fluid compressibility. Worse conditions are for gases and liquid hydrogen in a cryogenic turbo pump. In aerostatic bearings pockets are not machined to reduce (eliminate) pneumatic hammer For LH, very shallow pockets and reduced pocket area are recommended. 37

38 Hydrostatic Bearings for Cryogenic Turbo Pumps Radial hydrostatic bearings Thrust hydrostatic bearing Figure 3 Advanced Liquid Hydrogen Turbopump [] 38

39 Hydrostatic Bearings for Cryogenic Turbo Pumps Radial hydrostatic bearing Thrust hydrostatic bearing Radial hydrostatic bearing for LH TP - Knurled surface θ Ω pocket Y journal orifice Figure 4 Hydrostatic radial and thrust bearings for cryogenic turbopump 39

40 40 Bulk-flow Analysis of Hydrostatic Bearings ( ) ( ) 0 = + + t h hv z hv z = z V V V t V h U V h P h z J ρ κ κ μ = z V V V t V h V h z P h z z z z z ρ κ μ Flow Continuity Circumferential Momentum transport Aial momentum transport -Turbulent flow with fluid inertia effects -Mean flow velocities average across film (h) - No accounting for strong recirculation zones Y pocket orifice journal Ω θ Y pocket orifice journal Ω θ

41 Bulk-flow Analysis of Hydrostatic Bearings MR Ps Supply pressure Pocket pressure field with angled injection P s Feed orifice and Supply volume PR, recess pressure HR PR + R P R P Film land Fluid flow, M Γ Film land Pa b ΩR H b Figure 6: Turbulent flow pressure distribution in a pocket of a hybrid bearing Flow continuity M R 1/ ρ = Cd Ao s R Γ t [ P P ] = M + ( ρv ) R Pressure rise before edge P + R = P R + μ κ b ( h + h ) R R Ω R V Pressure rise at edge P R P (1 ) + ξ ρe + ρ 1 ρe + = R + h h + h R V, z Figure 6 Pocket pressures: angled & radial injection 41

42 Bulk-flow Analysis of Hydrostatic Bearings Small amplitude radial motions (,Y) at frequency (ω) to derive zeroth order equations for equilibrium flow field: flow rate, load capacity, power loss, temperature raise first-order equations for perturbed flow field: (stiffness, damping and inertia) force coefficients Z αβ = { P H } β α R dz dθ = Kαβ ω M αβ + iω Cαβ ; α, β =, Y A B Numerical method of solution: SIMPLEC method, etension of control volume method, + component method for superposition of hydrostatic and hydrodynamic effects. Sensitivity Analysis Bearing force coefficients and performance parameters are most sensitive to orifice entrance loss coefficient. Numerical Analysis : Hydrostatic Bearings 4

43 Dynamic Performance of Hydrostatic Bearings Eample: Water bearing replacing oil lubricated bearing Fluid: water at 30 C ( 0.79 cpoise, 995 kg/m3) D=L = mm (6 inch) c=0.10 mm (4 mil), nominal clearance 5 pockets: l=51 mm, arc 41, depth=0.381 mm Orifice diameter: 3. mm (Cd=0.80) Static load = 5000 N smooth rotor and stator surfaces Nominal speed = 3600 rpm, Pressure drop 34.4 bar C = 1.33 oil bearing Pocket depth/c = 3.75 Pocket area = 19% to avoid hammer STATIC LOAD FROM PUMP WEIGHT Pressure supply ~ RPM (bleed off from pump discharge) Table Inlet loss coefficient ξ=0.1 Inlet swirl α=0.50 RADIAL AND TANGENTIAL INJECTION Geometry and operating conditions of HJBs for a liquid pump Influence on cross-coupled stiffness and stability 43

44 Hydrostatic Bearing Orifice diameter selection HJB design: At nominal operating condition Ps-Pa=34.4 bar, 3600 rpm L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg) HJB design: At nominal operating condition Ps-Pa=34.4 bar, 3600 rpm L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg) Design K (MN/m) Ky (MN/m) 350 = Kyy K=Kyy K (MN/m) Ky (MN/m) K-M w^ Stiffness coefficients K=Kyy = Kyy Ky = -Ky Ky=-Ky Stiffness coefficients K - M ω Ky=-Ky = mm Selected orifice diameter Orifice diameter (mm) Orifice diameter Pocket pressure ratio 3.0 mm Selected orifice diameter Pocket pressure ratio Select diameter - Operating condition:.6 krpm, 34.4 bar pressure supply (NO LOAD) - Select orifice diameter to MAIMIZE direct stiffness - No influence of angled injection on K Figure 7 Direct and cross-coupled stiffnesses versus orifice diameter and pocket pressure for water hydrostatic bearing. Nominal operating condition, centered bearing (no load) 44

45 Hydrostatic Bearing Orifice diameter selection Parameters HJB design: Design Pocket pressure ratio HJB flow rate (kg/s) Power (kw) At nominal operating condition Ps-Pa=34.4 bar, 3600 rpm flow Drag power (kw) L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg) Flow rate (kg/s) Supply pressure Pocket pressure ratio Parameters HJB design: Damping M = Myy At nominal operating condition Ps-Pa=34.4 bar, 3600 rpm selected design Inertia My = -My L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg) M (kg) My (kg) C (kns/m) Cy (kns/m) C = Cyy Cy = Cy selected orifice diameter Orifice diameter (mm) Orifice diameter Orifice diameter (mm) Orifice diameter Selected diameter - Drag power, flow rate and pocket pressure increase with orifice diameter - Direct damping and inertia coefficients decrease Figure 8 Performance parameters for water hydrostatic bearing versus orifice diameter. Nominal operating condition, centered bearing (no load) 45

46 Hydrostatic Bearings Static Load Performance Operating journal eccentricity L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm Attitude angle L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm operation operating condition, Ps-Pa=34.4 bar [deg] operating condition, Ps-Pa=34.4 bar Radial e/c [fraction of clearance] STATIC LOAD = 5 kn Rotor Speed (RPM) tangential injection radial injection 15 Tangent tangential injection 10 y radial injection 5 load direction STATIC LOAD = 5 kn Rotor Speed (RPM) RPM & Psupply RPM & Psupply Load (W)=5 kn - At operating condition, static eccentricity is small, 10% of clearance (c=0.10 mm) - Large eccentricities at low speeds because pressure supply is low (hydrodynamic operation) -Tangential injection reduces attitude angle: will result in improved stability of bearing Figure 9 Journal eccentricity and attitude angle versus rotor speed. Water hydrostatic bearing with radial and tangential injection 46

47 Hydrostatic Bearings Peak pressures Ma film pressures L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm Mass flow rate L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm [bar] operating condition, Ps-Pa=34.4 bar supply pressure function of pump speed operation [kg/s] flow operating condition, Ps-Pa=34.4 bar 50.0 Psupply.00 R & Ang Radial Tangent tangential injection radial injection Supply pressure 0.50 tangential injection radial injection STATIC LOAD = 5 kn Rotor Speed (RPM) STATIC LOAD = 5 kn Rotor Speed (RPM) RPM & Psupply RPM & Psupply Load (W)=5 kn - Flow rate is proportional to rotor speed since supply pressure (~ RPM ) - Ma. film pressure is proportional to supply pressure, Ma. Pressure ~ RPM - Tangential injection increases edge recess pressure no influence on flow rate - Large flow rate (90 LPM) typical of application 1/ Figure 30 Maimum film pressures and flow rate versus rotor speed. Water hydrostatic bearing with radial and tangential injection 47

48 Hydrostatic Bearings Drag Torque Drag Torque L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm Drag Power L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm [N-m] operating condition, Ps-Pa=34.4 bar operation [kw] operating condition, Ps-Pa=34.4 bar 1.00 Radial 6.00 Radial Tangent tangential injection.00 Tangent tangential injection.00 radial injection 1.00 radial injection STATIC LOAD = 5 kn Rotor Speed (RPM) STATIC LOAD = 5 kn Rotor Speed (RPM) RPM & Psupply RPM & Psupply Load (W)=5 kn - Drag torque & power proportional to RPM - Tangential injection decreases power & torque since it retards development of circumferential speed. Care at low speeds and high pressures (reverse journal rotation) Figure 31 Torque and drag power versus rotor speed. Water hydrostatic bearing with radial and tangential injection 48

49 Hydrostatic Bearings STIFFNESSES Direct stiffnesses K, Kyy L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm Cross stiffnesses Ky, -Ky L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm 900 operating condition, Ps-Pa=34.4 bar [MN/m] 800 operation y Tangent Radial K: tangential injection 00 radial injection Kyy tangential injection 100 radial injection STATIC LOAD = 5 kn Rotor Speed (RPM) RPM & Psupply [MN/m] STATIC LOAD = 5 kn operating condition, Ps-Pa=34.4 bar y Rotor Speed (RPM) Ky: tangential injection radial injection -Ky tangential injection Tangent radial injection radial injection Radial tangential injection RPM & Psupply Load (W)=5 kn - At low speeds, bearing operates under hydrodynamic conditions since feed pressure is too low. All coefficients are large since operating eccentricity (e/c) is large - At operating speed, direct stiffness K~KYY & KY=-KY since (e/c)~0 : near centered operation. - Tangential injection reduces greatly cross-coupled stiffness. Figure 3 1 Stiffness coefficients versus rotor speed. Water hydrostatic bearing with radial and tangential injection 49

50 Hydrostatic Bearings DAMPING Direct damping C, Cyy L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm Cross damping Cy, -Cy L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm [kns/m] y operating condition, Ps-Pa=34.4 bar C: tangential injection radial injection Cyy tangential injection radial injection [kns/m] Different scale operating condition, Ps-Pa=34.4 bar operation Cy: tangential injection radial injection -Cy tangential injection radial injection radial injection Radial Tangent Radial y Tangent tangential injection STATIC LOAD = 5 kn Rotor Speed (RPM) RPM & Psupply STATIC LOAD = 5 kn Rotor Speed (RPM) RPM & Psupply Load (W)=5 kn - At low speeds, all coefficients are large since operating eccentricity (e/c) is large (Hydrodynamic operation) - At operating speed, direct damping C~CYY & CY=-CY since (e/c)~0 : near centered operation. - From moderate to high speeds, C > CY - Tangential injection reduces cross-coupled damping small effect on rotordynamics Figure 33 1 Damping coefficients versus rotor speed. Water hydrostatic bearing with radial and tangential injection 50

51 Hydrostatic Bearings ADDED MASS Direct inertia M, Myy L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm Cross-inertia My, -My L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm [kg] Tangent operation Radial 5 [kg] Different scale 0 My: tangential injection radial injection operating condition, Ps-Pa=34.4 bar M: tangential injection radial injection Myy tangential injection 15 +My tangential injection -My radial injection Radial 80 radial injection operating condition, Ps-Pa=34.4 bar y 5 y Tangent STATIC LOAD = 5 kn Rotor Speed (RPM) RPM & Psupply STATIC LOAD = 5 kn Rotor Speed (RPM) RPM & Psupply Load (W)=5 kn - Large fluid inertia effect (~ 160 kg) >> kg = solid steel piece (L,D) - Direct inertia changes little with rotor speed - At operating speed, direct inertia M~MYY & MY=-MY since (e/c)~0 : near centered operation. - For all speeds, M > MY - Tangential injection reduces cross-coupled inertia small effect on rotordynamics Figure 34 1 Fluid inertia coefficients versus rotor speed. Water hydrostatic bearing with radial and tangential injection 51

52 Whirl Frequency Ratio & Critical mass Whirl frequency ratio [-] operating condition, Ps-Pa=34.4 bar L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm Radial tangential injection Critical mass [kg] operating condition, Ps-Pa=34.4 bar Tangent L=D=0.15 m, c=10 um, 5 pocket (l=l/3, arc =4 deg), orifice do=3. mm Tangent Fully stable WFR =<0 operation Rotor Speed (RPM) radial injection tangential injection against shaft rotation RPM & Psupply tangential injection radial injection Radial Rotor Speed (RPM) STATIC LOAD = 5 kn RPM & Psupply Load (W)=5 kn - WFR ~ 0.60 for radial injection bearing, Critical mass ~ 8,000 kg - With tangential injection: WFR drops rapidly towards 0.10 at operating point and beyond. Critical mass at least 10 larger than for radial injection - In other applications (e: LO bearing), benefit of tangential injection is lost at very high speeds when hydrodynamic effects dominate flow -Critical mass results applicable to RIGID ROTOR only Figure 35 Whirl frequency ratio & Critical Mass versus rotor speed. Water hydrostatic bearing with radial and tangential injection 5

53 Hydrostatic Bearings Recommendations Hydrostatic bearings have WFR > ~ 0.50 limiting their application to ~ critical speed. Limiting speed condition can be worse if fluid is compressible and pockets are too deep & large area. To reduce risk of hydrodynamic instability & increase bearing stability margin: -Teture bearing surface Proven with macro rough surfaces such as Knurled, round hole and tire truck pattern tested successfully -Angled injection against rotation Retards circumferential flow swirl, effectiveness reduces at high rotor speeds, Can induce backward whirl. Tested successfully -Bearing asymmetry Geometrically induce stiffness orthotropy (K > KYY) Aial feed grooves, mechanical preload, etc. Tested & patented! 53

54 Hydrostatic Bearings Recommendations Fleure-pivot Tilting pad hybrid bearing Tilting pads accommodate shaft motions to load direction, no generation of cross coupled stiffnesses, KY ~ KY ~ 0. No stability margin. Wire EDM construction allows for reliable hydrostatic feeding. Tested in water, oil and gas applications 54

55 Hydrostatic Bearings for Cryogenic Turbo Pumps To avoid pneumatic hammer: * reduce area pocket/land area to ~ 15-5% * pocket depth to clearance ratio ~ 10 or less * design and construct orifices without supply discharge volume (no pressure recovery zone) P a L Film land P s Q r P R, recess pressure Feed restrictor L b Fluid flow, Ql P a h p h Design parameter, ΔP < < 1, TYP 0.1 or less DP = (PR -PA) 3 Npocket (Vpocket+Vsupply orifice) Kfluid (Z+1) Area_bearing Cradial_clearance Kfluid: Fluid Bulk modulus Area_bearing ~ π D L Z= (PR -PA) a (PS -PR) a= for orifice restrictors PS, PR, PA: supply, recess or pocket, discharge pressures 55

56 Hydrostatic Bearings for Cryogenic Turbo Pumps Cryogenic fluid hydrostatic bearing design: * small pocket area (15-5 % of total area) * shallow pocket depth * small or null orifice discharge volume Application: high surface speeds, low and high frequencies, compressible liquids (LO, LH, LN) + Angled injection against rotation to reduce cross-coupled stiffnesses (avoid hydrodynamic instability) Nearly inherent restrictor type, i.e. orifice coefficient regulated by clearance 56

57 Gas hydrostatic bearing design * Null pocket area (0 % of total area) * Inherent restrictor type, i.e. orifice coefficient regulated by clearance Applications: low and high surface speeds, low and high frequencies, All Gases (air, GO, GH, GN) + angled injection against rotation to reduce cross-coupled stiffnesses 57

58 Hydrostatic Bearings Model Validation HYDROJET radial hydrostatic bearings Tests at TAMU with water (1000 psi (70 bar) ma, 5 krpm ma). + 0 bearings 3 clearances & pocket depths, different pocket shapes, macro-roughness (surface tetured) bearings, angled injection. Gas Honeycomb seals Water Lomakin Bearings (Snecma-SEP) Oil tilting and fleure pivot journal bearings HYDROTHRUST aial thrust hydrostatic bearings NONE available in literature for high speed, high pressure (turbulent flows) Concerns: centrifugal and advection fluid inertia cause severe fluid starvation in bearing and reduced aial stiffness coefficients due to effect of added mass coefficients TESTs verified predictions 58

59 Needs in turbomachinery largest power output to weight ratio, reliability and performance, compact with low number of parts, etreme temperatures and pressures, Rotordynamics low friction and wear automated agile processes coatings: nanopowders surface conditioning environmentally safe and friendly. oil-free machinery inert gas buffer sealing Desired features of support elements (bearings and seals) High stiffness and damping coefficients Linearity with respect to amplitudes of rotor motion Avoidance of rotordynamic instability due to hydrodynamic effects Controllable features to avoid surge/stall, etc. 59

60 Hydrostatic Bearings Learn more See Publications For complete list of computational model predictions and comparisons to test data (over 30 journal papers and 10+ technical progress reports to NASA, USAF, P&W, Rocketdyne, Snecma-SEP, Northrop Grumman) 60

61 Bulk-flow Analysis of Hydrostatic Bearings At Teas A&M: Hydrojet & Hydrothrust Equations for flow in film lands of bearing Equations for flow in pockets of hydrostatic bearing Flow conditions Mass conservation, Bulk-Flow momentum in circumferential and aial directions (D), Energy transport for mean flow temperature Various surface temperature models Fluid inertia effects at entrance and eit flow regions. Global mass conservation: orifice inlet flow, flow from recess towards or from film lands, and rate of accumulation of fluid within pocket volume, Global momentum in circumferential direction due to angled injection. Global energy transport with adiabatic heat flow surfaces Laminar, laminar to turbulent transition and fully developed turbulent bulk-flow model. Turbulent flow closure model: Moody's friction factor including surface roughness. Fluid with variable properties f(p,t) Model for Cryogenic Hydrostatic Bearings 61

62 Hydrostatic Bearings Funding & Work to Date 40 k, Rocketdyne ( ), 110 k, Pratt & Whitney (1991-9), 360 k, NASA GRC ( ), 10 k, NASA MSFC (1998/99-001/) 9 k, Norhtop Grumman ( ) - (USET Program) Separate funding for performance evaluation and rotordynamics measurements for validation of radial bearing tool prediction All US turbo pump manufacturers and NASA, including SNECMA-SEP, use Hydrojet and Hydrothrust to model cryogenic fluid film bearings and seals. Other industries and Universities have benefited from technology. USET Program ( ) CLIN (a) non-linear forced response of fluid film bearing (98.5 k) CLIN (b) mied flow regime lift off response (130.5 k) CLIN Eperimental Study of Hydrostatic / Hydrodynamic Thrust Bearings (788 k) 6

63 Hydrostatic Bearings CFD models 3D CFD modeling of flow and pressure in POCKETS carried out by P&W (90 s) and also by Universite de Poitiers funded by Snecma- SEP (France, ). OBJECTIVEs: Predict comple flow field in pocket and etract empirical parameters for pressure loss at inlet to film lands and for development of pressure profile for angled injection bearings. Insert empirical parameters into D-bulk-flow codes for prediction of bearing rotordynamic force coefficients. Best published work: Mihai ARGHIR, Université de Poitiers, France. FINDINGS: 3D-CFD predictions are NOT better than D-bulk flow predictions when compared to test data (TAMU-Childs). TAMU codes are still unsurpassed in terms of accuracy of predictions and speed of eecution. 63

64 Annular Pressure Seals BACK UP slide Incompressible fluid, turbulent flow V z = ρ (1 + P s P ζ ) + a L ρ c f z Aial velocity (leakage) decreases with increase of inlet loss (ζ) and friction factor (f) and length of land in seal. P e P a = 1 + P s P a (1+ ζ ) f z c L Entrance pressure into seal decreases as inlet loss (ζ) increases and as land friction factor (f) decreases or land length increases The Lomakin effect 64