- •Chapter I introduction
- •1. The subject of hydraulics
- •2. Historical background
- •3. Forces acting on a fluid. Pressure
- •4. Properties of liquids
- •Chapter II hydrostatics.
- •5. Hydrostatic pressure
- •6. The basic hydrostatic equation
- •7. Pressure head. Vacuum. Pressure measurement
- •8. Fluid pressure on a plane surface
- •Fig. 12. Pressure distribution on a rectangular wall
- •9. Fluid pressure on cylindrical and spherical surfaces. Buoyancy and floatation
- •Fig. 18. Automatic relief valve.
- •Relative rest of a liquid
- •10. Basic concepts
- •11. Liquid in a vessel moving with uniform acceleration in a straight line
- •12. Liquid in a uniformly rotating vessel
- •The basic equations of hydraulics
- •13. Fundamental concepts
- •14. Rate of discharge. Equation of continuity
- •15. Bernoulli's equation for a stream tube of an ideal liquid
- •16. Bernoulli's equation for real flow
- •17. Mead losses (general considerations)
- •18. Examples of application of bernoulli's equation to engineering problems
- •Chapter V flow through pipes. Hydrodynamic similarity
- •19. Flow through pipes
- •20. Hydrodynamic similarity
- •21. Cavitati0n
- •Chapter VI laminar flow
- •22.Laminar flow in circular pipes
- •23. Entrance conditions in laminar flow. The α coefficient
- •24. Laminar flow between parallel boundaries
- •Chapter VII turbulent flow
- •25. Turbulent flow in smooth pipes
- •26. Turbulent flow in rough pipes
- •27. Turbulent flow in noncircular pipes
- •Chapter VIII local features and minor losses
- •28. General considerations concerning local features in pipes
- •29. Abrupt expansion
- •30. Gradual expansion
- •31. Pipe contraction
- •32. Pipe bends
- •33. Local disturbances in laminar flow
- •34. Local features in aircraft hydraulic systems
- •Chapter IX flow through orifices, tubes and nozzles
- •35. Sharp-edged orifice in thin wall
- •36. Suppressed contraction. Submerged jet
- •37. Flow through tubes and nozzles
- •38. Discharge with varying head (emptying of vessels)
- •39. Injectors
- •Relative motion and unsteady pipe flow
- •40. Bernoulli's equation for relative motion
- •41. Unsteady flow through pipes
- •42. Water hammer in pipes
- •Chapter XI calculation of pipelines
- •43. Plain pipeline
- •44. Siphon
- •45. Compound pipes in series and in parallel
- •46. Calculation of branching and composite pipelines
- •47. Pipeline with pump
- •Chapter XII centrifugal pumps
- •48. General concepts
- •49. The basic equation for centrifugal pumps
- •50. Characteristics of ideal pump. Degree of reaction
- •51. Impeller with finite number of vanes
- •52. Hydraulic losses in pump. Plotting rated characteristic curve
- •53. Pump efficiency
- •54. Similarity formulas
- •55. Specific speed and its relation to impeller geometry
- •56. Relation between specific speed and efficiency
- •57. Cavitation conditions for centrifugal pumps (according to s.S. Rudnev)
- •58. Calculation of volute casing
- •59. Selection of pump type. Special features of centrifugal pumps used in aeronautical and rocket engineering
51. Impeller with finite number of vanes
So far we have been investigating the performance of an idealised centrifugal pump with an infinite number of vanes and unity efficiency. The physical meaning of these assumptions was examined in Sec. 49.
In going over to real pumps we shall begin with eliminating the first assumption, retaining the second for the time being.
Thus, a pump with a finite number of vanes. Real pumps usually have from six to twelve vanes. The relative flow through the vane passages is not so laminar as assumed before and the velocity distribution is not uniform, On the leading surface, of the vane, denoted by a "plus" sign in Fig. 136a, the pressure is higher and the velocity lower, and the velocity distribution in the passage is approximately as shown.
The velocity distribution can be regarded as the resultant of two flows: one with uniform velocity distribution, as was the case when
z=oo (Fig. 1366), and a rotational flow inside the passage in the opposite direction of the rotation of the impeller (Fig. 136c). In pure form the rotational flow is present when the discharge through the impeller is zero (Q = 0).
In view of the nonuniformity of the distribution of the relative and absolute velocities in the vane passages when the number of vanes is unite, the mean velocity for a circle of given radius is in troduced. Our interest is the mean value of the tangential component of the absolute exit velocity ишЧ which determines the head developed by the pump. This component is smaller for a finite number of vanes than for an infinite number because the less the number of vanes the less the whirl imparted to the fluid by the impeller. In the absence of vanes (z = 0) the whirl is zero, i. e., v%a = 0, and the fluid (in the ideal case) issues from the impeller in a radial direction.
A reduction of the velocity v2u in passing over to a finite number of vanes is also accounted for by the prerotation mentioned before. This relative motion gives rise to an additional absolute velocity hv2u at the outer periphery of the impeller (see Fig. 136c), which is directed opposite to v2u and, hence, is subtracted from the latter.
Owing to this the velocity triangle at the impeller exit changes. In Fig. 137, the solid lines give the velocity vectors when the number of vanes is infinite and the broken lines are the velocity vectors for a finite number. The construction was made for identical values of u2 and v2r i. e., for identical rotational speeds and rates of discharge. The primed values are for the case of a finite number of
vanes.
A reduction of the tangential component v2u in transition to a finite number of vanes results in a drop in the pumping head. The head that would have been generated by a pump if there were no head losses inside the pump is called the theoretical, or ideal, head, denoted Htz. From Eq. (12.8), we have
We shall call the ratio of Htz to Hz the vane-number coefficient:
whence the head in question Is
The problem now is to determine the numerical value of \x. Obviously, the coefficient depends first and foremost on the number of vanes 2, though it is also affected by the length of the Vanes, which
depends on the ratio — and on the angle of inclination of the
vanes p2- *
Theoretical investigations reveal that*-u-dow not depend on the operating conditions of a pump, i; e., on 0, Hptttl^ or n. It is wholly determined by impeller geometry and is constant for a given impeller.
Without going into the theory of the effect of the number of vanes on the head, here is the conclusion of this theory as represented by a formula for ix:
where
Here, for example, is the value of μ for β2 = 30° and = 0.5
Table 6
z |
4 |
6 |
8 |
10 |
12 |
16 |
24 |
μ |
0.624 |
0.714 |
0.768 |
0.806 |
0.834 |
0.870 |
0.908 |
Thus, at
As the ratio between Htg and Ht(g> is constant for a given pump, the theoretical characteristic curve for a finite number of vanes, like the characteristic curve of an idealised pump with a uniform speed of rotation (n = const), is a straight line. At β2 90°, it is parallel to the characteristic curve of an idealised pump, and at β2 < 90° it intersects the latter on the axis of abscissas, as Htz = 0 and Ht>= 0 at the same discharge
This follows from Eqs (12.12) and (12.18).