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Research Papers

Effect of Reynolds Number, Hole Patterns, and Target Plate Thickness on the Cooling Performance of an Impinging Jet Array—Part II: Conjugate Heat Transfer Results and Optimization

[+] Author and Article Information
Weihong Li

Department of Thermal Engineering,
Gas Turbine Institute,
Tsinghua University,
Beijing 100084, China
e-mail: Liwh13@mails.tsinghua.edu.cn

Li Yang

Department of Mechanical Engineering and Material Science,
University of Pittsburgh,
Pittsburgh, PA 15213

Xueying Li

Department of Thermal Engineering,
Gas Turbine Institute,
Tsinghua University,
Beijing 100084, China
e-mail: lixueying@mail.tsinghua.edu.cn

Jing Ren

Department of Thermal Engineering,
Gas Turbine Institute,
Tsinghua University,
Beijing 100084, China
e-mail: renj@tsinghua.edu.cn

Hongde Jiang

Department of Thermal Engineering,
Gas Turbine Institute,
Tsinghua University,
Beijing 100084, China

1Corresponding author.

Contributed by the International Gas Turbine Institute (IGTI) of ASME for publication in the JOURNAL OF TURBOMACHINERY. Manuscript received July 1, 2016; final manuscript received March 7, 2017; published online May 9, 2017. Editor: Kenneth Hall.

J. Turbomach 139(10), 101001 (May 09, 2017) (13 pages) Paper No: TURBO-16-1140; doi: 10.1115/1.4036297 History: Received July 01, 2016; Revised March 07, 2017

This study comprehensively illustrates the effect of Reynolds number, hole spacing, nozzle-to-target distance, and target plate thickness on the conjugate heat transfer (CHT) performance of an impinging jet array. Test models are composed of a specific thermal-conductivity material which exerts a matched model Biot number to that of engine condition. High-resolution temperature measurements are conducted on the impinging-target plate utilizing steady liquid crystal (SLC) with Reynolds numbers ranging from 5000 to 27,500. Different streamwise and spanwise jet-to-jet spacing (i.e., X/D and Y/D: 4–8), nozzle-to-target plate distance (Z/D: 0.75–3), and target plate thickness (t/D: 0.75–2.75) are employed to compose a total of 108 different geometries. Experimental measured temperature is utilized as boundary conditions to conduct finite element simulation. Local and averaged nondimensional temperature and averaged temperature uniformity of target plate “hot side” are obtained. Optimum hole spacing arrangements, impingement distance, and target plate thickness are pointed out to minimize hot side temperature, amount of cooling air and to maximize temperature uniformity. Also included are 2D predictions with different convective boundary conditions, i.e., local 2D distribution and row-averaged heat transfer coefficients (HTCs), to estimate the accuracy of temperature prediction in comparison with the conjugate results.

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Figures

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Fig. 1

Double-wall cooling vane with multiple impinging jets [8]

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Fig. 2

Impingement cooling test facility

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Fig. 3

Schematic representative of test models

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Fig. 4

Comparison of: (a) spanwise average and (b) area average Nusselt number with literature data

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Fig. 5

Local nondimensional temperature distribution for different Re values. (px, py, pz, t/D) = (6, 6, 2, 1.75).

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Fig. 6

Spanwise-averaged nondimensional temperature distribution for different Re values. (px, py, pz, t/D) = (6, 6, 2, 1.75).

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Fig. 7

Local nondimensional temperature distribution for different px values. (py, pz, t/D, Re) = (4, 2, 0.75, 10 K).

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Fig. 8

Spanwise-averaged nondimensional temperature distribution for different px values. (py, pz, t/D, Re) = (4, 2, 0.75, 10 K).

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Fig. 10

Spanwise-averaged nondimensional temperature distribution for different py values. (px, pz, t/D, Re) = (6, 2, 0.75, 10 K).

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Fig. 9

Local nondimensional temperature distribution for different py values. (px, pz, t/D, Re) = (6, 2, 0.75, 10 K).

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Fig. 11

Local nondimensional temperature distribution for different impingement distance pz. (px, py, t/D, Re) = (6, 6, 1.75, 10 K).

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Fig. 12

Spanwise-averaged nondimensional temperature distribution for different impingement distance pz. (px, py, t/D, Re) = (6, 6, 1.75, 10 K).

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Fig. 13

Local nondimensional temperature distribution for different target plate thickness t. (px, py, pz, Re) = (6, 6, 2, 10 K).

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Fig. 14

Spanwise-averaged nondimensional temperature distribution for different target plate thickness t. (px, py, pz, Re) = (6, 6, 2, 10 K).

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Fig. 15

An overall estimation of Reynolds number, hole pattern, and target plate thickness on (a) area-averaged nondimensional temperature θ and (b) area-averaged relative standard deviation of θ

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Fig. 16

Area-averaged nondimensional temperature θ as a function of Gs at various Reynolds numbers. (pz, t/D) = (0.75, 1.75).

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Fig. 17

Area-averaged nondimensional temperature θ as a function of Gs at various Reynolds numbers. (pz, t/D) = (1.2, 1.75).

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Fig. 18

Area-averaged nondimensional temperature θ as a function of Gs at various Reynolds numbers. (pz, t/D) = (2, 1.75).

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Fig. 19

Area-averaged nondimensional temperature θ as a function of Gs at various pz and t/D values

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Fig. 20

Area-averaged RSD as a function of Gs at various pz and t/D values

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Fig. 21

Local nondimensional temperature distributions of external side of target plate predicted by different thermal boundary conditions. (px, py, pz, t/D, Re) = (8, 4, 2, 0.75, 20,000).

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Fig. 22

Spanwise-averaged nontemperature distributions of external side of target plate predicted by different thermal boundary conditions. (px, py, pz, t/D, Re) = (8, 4, 2, 0.75, 20,000).

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Fig. 23

Comparison of area-averaged θ of conjugate experiments with data predicted with (a) row-averaged heat transfer coefficients and (b) local heat transfer coefficients

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Fig. 24

Comparison of area-averaged RSD of conjugate experiments with data predicted with: (a) row-averaged heat transfer coefficients and (b) local heat transfer coefficients

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