- •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
39. Injectors
An injector is a specially designed tube or nozzle which atomises the discharged liquid, i.e., the jet into the atmosphere (or a space filled with gas under pressure) is broken up into a fine spray.
The most common type of injector used in gas-turbine aircraft and liquid-propellant rocket engines is the so-called swirl injector for spraying fuel in the combustion chamber.
In such an injector whirl is imparted to the stream, which is then contracted (Fig. 95). The angular momentum created by the tangential approach of the liquid remains approximately constant during flow through the injector. Consequently, as the stream converges the whirl velocity component increases considerably and large centrifugal forces develop which throw the liquid to the walls, forming a thin film which issues from the injector in a fine spray. Along the centre line of the injector there is formed an air (gas) vortex in which the pressure at the surface is close to atmospheric (if the discharge is into the atmosphere). This vortex is completely analogous to that formed when liquid flows out of a hole in the bottom of a vessel (Fig. 96), though in the injector it is much more intensive.
Thus, the jet issuing from a swirl injector does not fill the whole cross-section of the injector nozzle; it is annular, with an air vortex along the centre (Fig. 97). Therefore, the contraction coefficient ε of a swirl injector is usually much less than unity.
Because of this, and also because the resultant velocity of discharge V is directed at an angle to the cross-section of the injector (Fig. 95), the tangent of which is equal to the ratio of the whirl component и to the axial component v the coefficient of discharge is always much less than unity, varying within broad limits depending upon the geometry and relative dimensions of the injector.
In order to determine the rate of discharge of an injector according to the basic equation (9.6)
the precise value of the coefficient of discharge ц must be known.
The injector theory developed by Professor G. N. Abramovich enables |i to be determined from the dimensions and geometry of the injector. We shall consider this theory very briefly for the case of an ideal fluid. The following are the three initial equations:
(i) Bernoulli's equation between sections 1-1 and 2-2 (see Fig. 95):
or
where is the rated head;
v and и are the axial and whirl components of the velocity V at the boundary of the air vortex at section 2-2. (ii) The equation for the conservation of angular momentum of the fluid with respect to the centre line at the given cross-sections:
or
where r0 = radius of the air vortex at section 2-2.
(iii) The continuity equation between the sections*:
or
where
From the last expression we have
which gives, after substitution into the second equation,
Using the third equation instead of the foregoing one, we obtain
where is a parameter characterising the geometry of theinjector.
Substitution of the expression for и into Bernoulli's equation at (i) yields
whence
* Assuming a uniform distribution of the axial velocities about the annulaj cross-section at the injector outlet.
Now we can express the rate of discharge as the product of the velocity and the annular area of the stream at the injector outlet, i.e.,
Thus, the discharge coefficient of the injector is
(9.20)
The coefficient e, however, is unknown, as we do not know the dimensions of the air vortex (the radius rv for a given r0 and A). To determine it some additional condition must be introduced. Such a condition was put forward as a hypothesis by Prof. Abramovich, and later it was confirmed experimentally. He postulated that a steady vortex would be of such size as to ensure a maximum rate of discharge Q for a given head H or, in other words, the flow regime is such that a given discharge is produced by the least possible head.
Let us find the value of e corresponding to the maximum coefficient of discharge μ. For this differentiate the expression under the radical in Eq. (9.20) with respect to e and equate the derivative to zero:
whence
(9.21)
This formula can be used to plot 8 as a function olA. The curve can be used together with Eq. (9.20) to compute values of μ for a series of values of A and to plot a graph of μ as a function of A (Fig. 98).
The diagram shows that with A increasing the coefficient μ decreases. Physically this is explained by the fact that A increasing means a higher whirl velocity u at the injector outlet as compared with the entrance velocity ul and, consequently, a more intensive whirl of the fluid. This leads to a vortex of larger diameter and a smaller cross-sectional area of the stream, which means that more and more of the available energy H is dissipated on building up the whirl velocity. At A = 0 (R =0), μ = 1, i.e., there is no whirl and the injector works as an ordinary nozzle.
The foregoing equations can be used to determine the angle of divergence of the spray or flame of the injector (see Fig. 98). With A increasing angle a increases and the discharge coefficient drops. Therefore in injector design A must be so chosen as to ensure a sufficiently wide angle a (up to 60°) without reducing μ too much.
The injector theory set forth here is developed for the case of an ideal fluid. The effect of viscosity on injector performance is manifest in that the angular momentum is not uniform, diminishing towards the outlet.
Accordingly, the whirl velocity component at the outlet is usually smaller, and the discharge greater than in the case of an ideal fluid. At first glance this might seem paradoxical.
The effects of viscosity can be taken into account by introducing an equivalent parameter Aeg, which is determined from the formula
where Xt = friction factor of the injector, which can be taken from Table 5, depending on the Reynolds number computed for the diameter and velocity at the injector inlet.
Table 5
-
1.5x103
3 x103
5 x103
l x104
2 x104
5x104
0.22
0.11
0.077
0.055
0.04
0.03
The equivalent injector parameter Aeq thus computed is used to determine the discharge coefficient μ and the angle a taking into account viscosity according to Abramovich's diagram in Fig. 98, where Aeg now stands for A. Since as a rule Ae < A, the coefficient μ taking into account viscosity is somewhat greater, and the angle a is smaller, than in the case of an ideal fluid.
In many liquid-propellant rocket injectors whirl is imparted to the fluid by means of a two- or three-step helix built into the nozzle (Fig. 99).
The injector theory is valid in this case, the factor A being computed according to the formula
(9.22)
where rm = mean radius of helical groove;
Sn = area of flow cross-section normal to groove; n = number of coils; φ = helix angle.
In modern gas-turbine engines there are more commonly usedadjustable swirl injectors in which the coefficient of discharge (or the area of the outlet) varies automatically with the changing fuel pressure. Such nozzles enable the range of fuel supply to be increased for a given pressure range while maintaining the required quality of spraying.
Widely employed are twin-nozzle and two-stage injectors and injectors with by-pass arrangement. Common to them all is a valve device which opens (or closes) an auxiliary conduit when tjie pressure rises, thereby increasing the coefficient of discharge or the outlet area.
The twin-nozzle injector (Fig. 100) actually comprises two
injectors, one inside theother. At low pressures the valve is closed and the inner injector operates;when the pressure rises the valve opens and the second injector becomes operative. The supply of fuel increases sharply.
The two-stage injector (Fig. 101) has one nozzle and one swirl chamber with two inlet pipes. At low pressures the fuel is supplied through one pipe, at high pressures, through both. As a result, the parameter A decreases and the coefficient μ increases.
The by-pass injector (Fig. 102) is provided with a valve-controlleddrain. The lower the pressure the wider opens the valve; at peak pressure the valve is closed completely. Thus, at low pressure the intake velocity is higher, which is equivalent to a smaller inlet area, and this means an increase in the equivalent parameter Aeq and a reduction of μ. This is just what is needed to widen the discharge range.
These adjustable injectors can be calculated on the basis of Abramovich's theory, with due consideration of specific features (see examples).
Example 1. Plot the flow characteristics of a twin-nozzle injector (Fig. 100) showing the relationship between the rate of discharge and the pressure drop in the injector, if the second nozzle (the second channel) becomes operative at a pressure drop equal to Apn- The geometry of both channels (dimensions and parameters Ax and 42) and the flow characteristics pf the regulating valve are given. Solve the problem in general form.
Solution, (i) According to the given values of Ax and A% determine μJ and JX2 from the graph in Fig. 98. (ii) Applying the equations
plot the characteristics of the first and second conduits of the injector (Fig. 103).
(iii) Sum the characteristics of the control valve and the second conduit. In performing this operation remember that the pressure drop Ap in the second conduit is expended in the injector proper and in the valve. Therefore the ord i-nates of Ap must be summed for the given rates of discharge.
(iv) To obtain the total flow characteristic of the injector, sum the characteristics of the first and second conduits and the valve, and the rates of discharge (Fig. 103).
Example 2. Find the expression for the parameter Ax of a swirl injector with by-pass if the total input of fuel is , where Q, - is the discharge through the injector nozzle and Qbp is the by-pass aischarge (see Fig. 102).
Solution, (i) Introduce a by-pass coefficient kbp:
(ii) The supply of fuel through the input pipes is
(iii) The quantity of fuel passing through the injector nozzle is
Consequently
whence
(iv) Substituting the expression for vx into the angular momentum equation, and then into Bernoulli's equation, determine the velocity v in the same way as before:
(v) The fuel supply through the injector is
(vi) Comparing this equation with the expression (9.20)t we find that
C H A P T E R X