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Research Papers

Characterizing Flow Effects of Ported Shroud Casing Treatment on Centrifugal Compressor Performance

[+] Author and Article Information
George A. Christou

Department of Aeronautics and Astronautics,
Massachusetts Institute of Technology,
Cambridge, MA 02139
e-mail: gchristo@mit.edu

Choon S. Tan

Department of Aeronautics and Astronautics,
Massachusetts Institute of Technology,
Cambridge, MA 02139
e-mail: choon@mit.edu

Borislav T. Sirakov

Honeywell Turbo Technologies,
Torrance, CA 90504
e-mail: Bobby.Sirakov@Honeywell.com

Vai-Man Lei

Honeywell Turbo Technologies,
Torrance, CA 90504
e-mail: VaiMan.Lei@Honeywell.com

Giuseppe Alescio

Honeywell Turbo Technologies,
Torrance, CA 90504
e-mail: Giuseppe.Alescio@Honeywell.com

1Corresponding author.

Contributed by the International Gas Turbine Institute (IGTI) of ASME for publication in the JOURNAL OF TURBOMACHINERY. Manuscript received November 13, 2016; final manuscript received December 20, 2016; published online March 21, 2017. Editor: Kenneth Hall.

J. Turbomach 139(8), 081005 (Mar 21, 2017) (12 pages) Paper No: TURBO-16-1297; doi: 10.1115/1.4035664 History: Received November 13, 2016; Revised December 20, 2016

This paper presents an investigation of the effects of ported shroud (PS) self-recirculating casing treatment used in turbocharger centrifugal compressors for increasing the operable range. The investigation consists of computing three-dimensional flow in a representative centrifugal compressor with and without PS at various levels of approximations in flow physics and geometrical configuration; this provides an enabler for establishing the causal link between PS flow effects and compressor performance changes. It is shown that the main flow path perceives the PS flow as a combination of flow actuations that include injection and removal of mass flow and injection of axial momentum and tangential momentum. A computational model in which the presence of the PS is replaced by imposed boundary conditions (BCs) that reflect the individual flow actuations has thus been formulated and implemented. The removal of a fraction of the inducer mass flow has been determined to be the dominant flow actuation in setting the performance of PS compressors. Mass flow removal reduces the flow blockage associated with the impeller tip leakage flow and increases the diffusion in the main flow path. Adding swirl to the injected flow in the direction opposite to the wheel rotation results in an increase of the stagnation pressure ratio and a decrease of the efficiency. The loss generation in the flow path has been defined to rationalize efficiency changes associated with PS compressor operation.

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References

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Figures

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Fig. 1

Full wheel PS compressor computational domain; frozen rotor type interface between wheel and port-inlet domain (A and B) and between wheel and diffuser-volute domain (C)

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Fig. 2

Comparison between numerical and gas stand measurements πc (left) and η (right) for ported compressor

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Fig. 3

Single passage PS actuation model used for modeling flow at both PS outlet and slot or only at PS outlet (a); when flow is removed at PS slot or for the nonported compressor variant (b) is used

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Fig. 4

Compressor πc (left) and η (right) for PS actuation model and axisymmetric PS compressor at 0.84 Nref and 1.16 Nref

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Fig. 5

Effect of mass flow removal at PS slot on compressor πc at 1.16 Nref

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Fig. 6

Effect of mass flow removal at PS slot on compressor η at 1.16 Nref

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Fig. 7

Effect of increasing fraction of mass flow removed at PS slot on impeller blockage with respect to baseline nonported m˙in/m˙ref=0.85 OP at 1.16 Nref

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Fig. 8

Effect of mass flow removal at PS outlet on impeller Cp rise with respect to baseline nonported m˙in/m˙ref=0.85 OP at 1.16 Nref

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Fig. 9

Breakdown of inducer ΔCp rise between mass flow removal OP at m˙in/m˙ref=0.85 with φPS Slot=0.5 and baseline nonported compressor OP m˙in/m˙ref=0.85 at 1.16 Nref

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Fig. 10

Effect of mass flow removal on inducer blade loading for mass flow removal OP at m˙in/m˙ref=0.85 with φPS Slot=0.5 and baseline nonported compressor OP m˙in/m˙ref=0.85 at 1.16 Nref

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Fig. 11

Flow blockage at crossflow plane upstream of PS slot; nonported OP m˙in/m˙ref=0.85 (left) and mass flow removal OP m˙in/m˙ref=0.85 with φPS Slot=0.5 (right) at 1.16 Nref

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Fig. 12

Effect of mass flow removal on entropy flux upstream of impeller inlet (left) and inside wheel (right) with respect to baseline nonported m˙in/m˙ref=0.85 OP at 1.16 Nref

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Fig. 13

Effect of mass flow removal at PS slot on compressor stability at 1.16 Nref

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Fig. 14

Effect of mass flow injection at PS outlet on compressor πc (left) and η (right) at 1.16 Nref

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Fig. 15

Effect of angular momentum injection at PS outlet on compressor πc (left) and η (right) at 1.16 Nref

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Fig. 16

Contour of uθ/Utip indicating that the extent of the inducer recirculation zone increases when moving closer to OPs near surge at 1.16 Nref

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Fig. 17

Control volume upstream of impeller inlet

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Fig. 18

Effect of angular momentum injection on impeller entropy generation at 1.16 Nref

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Fig. 19

Combined effect of mass flow removal at PS slot and angular momentum injection at PS outlet on compressor πc (left) and η (right) at near surge OP at 1.16 Nref

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Fig. 20

Fraction of recirculating mass flow m˙PS/m˙ind for axisymmetric PS compressor at 1.16 Nref

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Fig. 21

Compressor πc (left) and η (right) for axisymmetric PS compressor and single passage PS actuation model with flow removal at PS slot at 1.16 Nref

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Fig. 22

Control volume used to separate static pressure rise; radially inward looking view

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