Method and Apparatus for in-Flight Combustion of Carbonaceous Fuels

In conventional slagging furnaces for steam generation and the like, solid carbonaceous fuels, such as crushed bituminous or semi-bituminous coal, are fed into a reaction or combustion zone. The combustion temperature is maintained at or above the ash fusion temperature in order to convert a major portion of the non-combustible ash present in the fuel to molten slag. Such furnaces have generally been relatively very large, having required the use of ceramic structures to prevent erosion of the combustion chamber by the higher temperature combustion products, have released large quantities of pollutants into the atmosphere, and have been severely limited as to the applications for which they could be utilized. The relatively large size of such furnaces has resulted in relatively high heat losses, lower overall thermal efficiency, and undesirably low power density, that is, thermal power output per unit of volume of the furnance.

One type of conventional slagging furnace is a so-called cyclone furnace, an example of which is disclosed in U.S. Pat. No. 2,357,301. In this cyclone furnace, crushed coal and oxidizer gas are both injected tangentially into the combustion chamber in a manner such that the gas, coal particles, and combustion products undergo high velocity cyclonic flow through the chamber. The non-combustibles present in the coal are centrifuged onto the combustion chamber wall to form a film of molten slag on the wall. A small quantity of relatively fine coal particles burn in their flight through the chamber while the vast majority of the coal is larger coal particles which are centrifuged onto the chamber wall. These larger particles adhere to the molten slag film on the wall and burn while on the wall.

In conventional cyclone furnaces this combustion of relatively-large, crushed-coal particles embedded in the slag on the combustion chamber walls tend to create a strongly reducing atmosphere in an annular region adjacent the walls. This is deleterious. Metal compounds (such as the iron oxides and sulfides commonly found in western American coals) are often reduced by this atmosphere thereby forming pools and puddles of liquid metal in the chamber-insulating slag layer. These puddles of liquid metal and sulfur compounds constitute, in effect, thermal short circuits through which extremely high heat flux may be conducted to the chamber wall, often resulting in overload of the cooling system and catastrophic melt-through of the metallic walls. In addition, the presence of sulfur compounds, with molten metal, may result in unacceptable corrosion phenomena.

One way of alleviating or avoiding the foregoing problems is to operate a conventional cyclone furnace with sufficient excess air to maintain an oxygen-rich stoichiometry near the combustion chamber wall. Operating a cyclone furnace with the large amounts of excess air required to avoid metal puddling and chemical corrosion is undesirable because doing so very significantly reduces the overall thermal efficiency of the boiler facility. In addition, a serious disadvantage of excess air combustion, in this age of stringent clean-air regulations, is that it results in excessive production of nitrogen oxides far exceeding the levels permitted by present day environmental standards.

We have invented a method and apparatus for combusting particulate solid carbonaceous fuel with improved efficiency, optimized energy recovery from the fuel, and increased power density. According to the invention, combustion occurs within a reaction chamber having a fluid-cooled wall surrounding and bounding the reaction zone. A relatively dense phase mixture of fuel particles and carrier fluid is injected into the reaction zone near the center of one end of the reaction chamber, and oxidizer gas is injected tangentially into the zone to establish high velocity swirling flow of the gas, fuel particles, and combustion products within an annular region of the reaction zone adjacent the chamber wall. The mass flow rates of the fuel and oxidizer gas are regulated to maintain a relatively oxygen-rich stoichiometry within this annular flow region and a relatively fuel-rich stoichiometry within a longitudinally extending central region of the reaction zone and to cause flow of the oxidizer gas and combustion products through the reaction zone with throughput residence times on the order of a few hundred milliseconds or less. It should be understood that the core portion is normally operated fuel-rich, i.e., at a stoichiometry less than 1.0; but the annular region is not necessarily maintained at a stoichiometry higher than 1.0. Rather, it is relatively oxygen-rich as compared to the stoichiometry of the core portion and as compared to the overall stoichiometry of the combustion in the first reaction zone. Thus, by the terms "relatively fuel-rich" and "relatively oxygen-rich" stoichiometries we mean that the core portion is fuel-rich as compared to the overall stoichiometry of the first reaction zone and the annular region is relatively oxygen-rich as compared to the same overall stoichiometry, even though it may have an absolute stoichiometry less than 1.0.

These stoichiometries, in the first combustion chamber, provide several beneficial effects: Substantially all of the carbon content of the fuel particles is converted to oxides of carbon while the particles are aerodynamically suspended in flight, before they reach the chamber walls and before they exit from the first combustion chamber. Relatively oxygen-rich stoichiometry in the annular portion, adjacent the slag layer, guards against formation of liquid metal puddles in the slag layer. Corrosion, that would result from the presence of sulfur compounds adjacent the metal walls, is avoided. Low stoichiometry combustion in the core portion mitigates against extreme temperature excursions in the gaseous combustion products, thereby limiting the production of nitrogen oxides (NO.sub.x). The foregoing benefits are realized without incurring the disadvantages associated with being obliged to use excess-air combustion overall.

The more fuel-rich stoichiometry in the central region of the reaction chamber results in lower combustion temperatures since the carbon content of the fuel is only partially oxidized, to carbon monoxide, within this region. The resulting carbon monoxide exits from the chamber with the other combustion products and may be subsequently combusted in a secondary combustion chamber such as the fire box of a boiler, kiln or furnace with the resultant conversion of the carbon monoxide to carbon dioxide. However, the combustion temperatures maintained in the first stage by this fuel-rich combustion are sufficient to fuse most non-combustibles in the fuel to molten slag without significant volatilization of the slag. This molton slag is centrifuged onto the reaction chamber wall which is fluid cooled to maintain a layer of solidified slag on the wall. The excess slag is drained from the chamber. The reduced temperatures that are consequent of fuel-rich combustion also result in reduced nitrogen oxide production.

Thus, in our combustion method and apparatus, the reaction chamber wall temperature and the combustion temperatures within the reaction zone are controlled so that most of the noncombustibles present in the fuel are fused, centrifugally deposited in a liquid state on the reaction chamber walls, and removed from the reaction zone, whereby most of the ash and slag in the fuel is separated from the gaseous combustion products by centrifugal action, without losing undesirably large fractions of unburned fuel in the slag. In addition, we may add sulfur capturing chemicals to the reaction zone which reduce pollutants in the exhaust gases. Our combustion apparatus is suitable for retrofitting heat energy facilities originally designed and constructed for consumption of natural gas or oil, and it may be used to provide hot-gas thermal power for other purposes such as kilns, furnaces and chemical processes such as the production of producer or synthesis gas. In any application, the space occupied by our combustion apparatus is small relative to conventional combustion apparatus having equivalent thermal power output. By maintaining high velocity flows in the combustion zone, so that throughput residence times are of the order of a few hundred milliseconds, a relatively small combustion chamber may be used to produce very high thermal power output levels. For example, a combustion chamber in accordance with our invention having a length of about six feet and a diameter of about thirty inches can be operated at a fuel-throughput power level of fifty million Btu per hour. This importantly facilitates the retrofitting of boiler plants originally designed to burn oil and/or gas, wherein the space available for installation of coal burning apparatus is commonly very severely limited.

Our preferred combustion apparatus has a generally cylindrical reaction chamber with a pintle valve near the center of one end of the chamber for injecting a dispersed dense phase mixture of particulate solid fuel and a carrier fluid, such as oxidizer gas or water, into the reaction zone. For most applications, the particles of fuel will be less than about 750 microns diameter. Suitable fuels are pulverized coal, comminuted oil-bearing shale, petroleum residuals, and the like. There is an oxidizer inlet opening tangentially into the chamber downstream of the pintle valve to introduce oxidizer gas such as air or pure oxygen tangentially into the reaction zone so as to establish in the reaction zone high velocity helical flow of the oxidizer gas, fuel particles, and combustion products within an annular region adjacent the surrounding cylindrical wall of the reaction chamber. An outlet downstream of this inlet provides means for exhausting from the chamber gaseous reaction products and any fine particles of slag which are not collected on the inner walls of the chamber. The mass flow rates of oxidizer gas and fuel to the reaction chamber are regulated to maintain a relatively oxygen-rich stoichiometry within the annular flow region adjacent the reaction chamber wall and a relatively fuel-rich stoichiometry within the longitudinally extending central region of the chamber, as discussed earlier.

As mentioned earlier, the particles of fuel are essentially completely reacted prior to their contact with the reaction chamber wall; this avoids burning of fuel particles on the chamber wall and thereby, also, alleviates the problem of iron puddling and chemical corrosion of the wall without the necessity of excess air combustion. Such complete fuel reaction is accomplished by maintaining a relatively oxygen-rich stoichiometry adjacent to the chamber wall and controlling the aeroballistic regime within the reaction zone so that the burn time of the particles is generally less than the flight time of the particles to the chamber wall. A primary feature of combustion in this aeroballistic regime is our ability to optimize mixing and modify the combustion process for variable combustion conditions such as carbon capture by the slag, turndown ratio, fuel type or composition, slag removal percentage, carbon burn-out efficiency, and combustion zone additives. Because of this feature, our apparatus is substantially smaller in size than burners having equivalent thermal power output, i.e., it features relatively very high power density.

The particular embodiments of the invention which are illustrated have inlets for injecting oxidizer gas into the reaction chamber as a plurality of separate streams. One inlet injects an oxidizer gas stream axially into the reaction zone in a direction substantially parallel to the longitudinal axis of the reaction chamber, and a second inlet injects an oxidizer gas stream tangentially relative to the wall of the chamber. By regulating the relative mass flow rates and velocities of these two gas streams and the fuel in to the chamber, including reducing the axial oxidizer gas stream to zero as discussed below, we are able to establish and maintain in-flight burning of the fuel particles. Specifically, we obtain flow of the oxidizer-fuel mixture through the reaction zone in a helical flow mode which may be what we refer to as wheel-type flow. By wheel-type flow we mean either a substantially pure wheel flow or a combined wheel-vortex flow. While the illustrated combustion apparatus has both axial and tangential oxidizer gas inlets to the reaction chamber to permit an establishment of a wide range of aeroballistic conditions in the reaction chamber, the optimum aeroballistic regime for combusting most types of carbonaceous coal fuels such as is obtained by utilizing tangential oxidizer gas injection only. In this case oxidizer gas flow into the reaction chamber through the axial oxidizer inlet is cut off so that all oxidizer gas flow to the reaction chamber occurs through the tangential oxidizer inlet.

The apparatus and its mode of operation are such that a major portion of the ash content of the fuel may be removed from the gaseous reaction products, as slag, before such products exit the reaction chamber. Specifically, in the preferred embodiment, the reaction chamber is provided with a slag baffle at the output end of the combustion zone. The wheel-type flow operates to transport slag droplets radially toward the reaction chamber walls near the downstream end of the reaction chamber, and the reaction temperatures within the reaction zone are maintained at levels such that slag volatilization is minimized. The fuel-rich stoichiometry in the central region of the reaction zone coupled with the absence of any need for excess air combustion permits these low combustion temperatures to be maintained. These relatively low temperature levels, in turn, result in reduced production of nitrogen oxides.

Up to about 95% of the slag is deposited on the walls and removed from the reaction zone as a liquid. Liquid state separation of the slag from the gaseous reaction products is controlled, at least partly, by controlling the relative input rates of fuel and air, and thereby controlling temperatures within the reaction zone. Liquid droplets of slag deposited on the inner surfaces tend to remain in liquid form and may be drained to the lower portion of the reaction chamber and removed through a slag trap or other appropriate means for removing the slag. In addition the use of a metallic water-cooled reaction chamber promotes the development of a layer of slag solidified on the inner surface of the reaction chamber.

Because the layer of solidified slag on the inner walls has a relatively low thermal conductivity, it serves as a liner which protects the internal chamber wall and reduces heat losses. The mechanisms for controlling fuel input and oxidizer input, taken together with the slag baffle and the water-cooled reaction chamber, constitute a means for minimizing the concentration of volatilized slag in the output gas stream and removing the bulk of the slag in liquid form.

For different operative modes, it is desirable to use different fuel dispersion patterns within the reaction zone. This is achieved by placing the fuel injection pintle valve in different locations or varying the spray angle at which fuel is injected relative to the longitudinal axis of the reaction chamber. In one preferred embodiment, the pintle valve assembly includes a coaxially positioned, longitudinally adjustable pintle having an enlarged terminal portion. A substantially conical surface on the enlarged terminal portion operates as a deflector for directing the input fuel radially outward from the pintle valve assembly in a generally cone-shaped dispersion pattern. The adjustment of fuel flow ratio is accomplished by a combination of two mechanisms. In the first, the ratio of fuel to carrier gas is varied by increasing or decreasing the carrier gas flow. Solid to gas ratios of up to about 20:1 and down to essentially all carrier gas enable throttling control over a wide range with no moving parts in the pintle valve. The second way to control fuel input is by longitudinal adjustment of the pintle valve.

One embodiment of our invention includes a second reaction chamber located immediately downstream from the slagging baffle of the first reaction chamber. This embodiment includes means for introducing additional oxidizer gas and mixing it with the gaseous reaction products exiting from the first reaction zone. By this arrangement, the first reaction zone may be operated fuel-rich so that the exhaust gases contain substantial quantities of incompletely combusted products such as carbon monoxide and hydrogen. In the second reaction chamber, these products are further reacted to produce additional thermal energy. Because up to 90% or more of the slag has been removed in the first reaction zone, the temperature in the second reaction chamber may be allowed to reach levels substantially higher than the slag volatilization temperature to thereby improve the thermodynamic efficiency in subsequently converting the thermal power to electrical power.

This embodiment of our apparatus includes, near the input end of the second reaction chamber, a reactant input device by which selected additional reactants may be added to the high temperature gas stream entering the second reaction chamber. In addition, the second reaction chamber may include arrangements for decreasing or eliminating the high angular velocity of the gaseous reaction products. In one preferred embodiment, modification of the angular velocity is accomplished by injecting a supplemental air in a direction and at a velocity such that the angular momentum of this additional oxidizer gas substantially counterbalances and offsets the angular momentum of the reaction products exiting from the first reaction zone. Such introduction of additional oxidizer gas into the second reaction chamber constitutes a means for deswirling, by momentum interchange, the gaseous reaction products.

In accordance with another feature of our invention, our reactants may be added to the reaction zone for such chemical reaction purposes as may be indicated by the chemistry of the particular type of reaction being conducted in the reaction zone. For example, additives may be used to render the slag more amenable to flowing at lower temperatures or to enhance capture of potential air pollutants which would otherwise be created in the burning process. By the addition of selected reactants, together with temperature control, sulfur oxides (SO.sub.x) effluents may be removed from the gaseous combustion products without the use of conventional stack-gas scrubber apparatus. To control SO.sub.x emissions, treatment chemicals such as carbonates may be added to the input fuel or introduced separately to the reaction chamber. The formation of nitrogen oxide (NO.sub.x) pollutants is controlled by maintaining fuel-rich combustion conditions and thereby limiting temperatures to levels low enough to prevent the rapid formation of NO.sub.x.

Another feature of our invention is that we are able to make producer gas or synthesis gas. We contemplate using our apparatus to burn carbonaceous fuels to make a type of producer gas which is fed to modified conventional oil or gas fired burners. It is desirable for such a producer gas to have the maximum amount of carbon monoxide obtainable. This increases its BTU content and, therefore, maximize its economic value. During periods of oil and gas shortages, our apparatus can thus be used to make a clean burning fuel which is a substitute for oil and natural gas.

A high-Btu synthesis gas may be produced by utilizing pure oxygen in place of air during the combustion process and injecting an amount of steam that will give the desired ratio of carbon monoxide and hydrogen in the synthesis gas. Using oxygen in place of air eliminates nitrogen which is a diluent and, in many instances, a deleterious component of synthesis gas. Because coal can be burned cleanly without our apparatus so that SO.sub.x and slag are removed from exhaust gases, our apparatus produces synthesis gas at a reduced cost compared to conventional processes.

In accordance with another feature of our invention, the apparatus may be used to generate high temperature exhaust gases which are utilized to process carbonaceous material such as coal, shale, or oil. A suitable system for producing such carbonaceous materials should include a first stage comprising our apparatus and one ore more stages coupled to our apparatus. The carbonaceous materials are fed into one or more of these downstream stages, and the exhaust gases flowing from the first stage or second stage into the subsequent stage or stages provide heat for processing the carbonaceous materials. Solids are separated from the gaseous components exiting the final stages of the system and volatile hydrocarbons are recovered. In processing coal, the hot gases will volatilize water and hydrocarbons in the coal. The valuable hydrocarbons would be recovered, and the remaining char, being a lighter weight, is more economically transported than the unprocessed coal. For example, coal comprises as much as 20-weight percent water. The cost of shipping coal containing such high qualities of water would more than offset the cost of treating the coal using our apparatus. When shale is retorted by heat processing, kerogen in the shale decomposes into oil, and the oil is then volatilized to separate it from the solid shale minerals. Oil is processed by flash cracking in which a feed stream of oil is injected into the downstream stages of the system and heated rapidly. The oil decomposes into lighter weight hydrocarbons which are then separated from the inert gaseous combustion products.

A more complete understanding of the present invention, as well as recognition of additional advantages, will be afforded to persons skilled in the combustion arts from consideration of the following detailed description of exemplary embodiments of our invention as illustrated in the appended drawings.

FIG. 1 is a schematic diagram of an apparatus in accordance with our invention.

FIGS. 2a through 2d are perspective illustrations of helical wheel-type flow realized in the apparatus of FIG. 1.

FIGS. 3 through 6 are graphs showing the characteristics of several different types of high velocity fluid flow and the motion of particles in a rotating fluid environment.

FIG. 7 is a perspective view, partially cut away, of an apparatus in accordance with our invention.

FIG. 8 is a side view, partially in section, of the apparatus shown in FIG. 7.

FIGS. 9 through 12 are cross-sectional views taken respectively at the planes, 9--9, 10--10, 11--11, and 12--12 of FIG. 8.

FIG. 13 is a schematic diagram of a dense phase reactant transport apparatus in accordance with our invention.

FIG. 14 is a side view partially in cross section of a portion of the apparatus of FIG. 13.

FIGS. 15 and 16 are side views partially in section of an alternative embodiment of a portion of the apparatus shown in FIGS. 7 and 8.

FIG. 17 is a longitudinal section through an alternative reaction chamber structure.

FIG. 18 is a cross-sectional view taken at the plane 18--18 of FIG. 17.

FIG. 19 is a partial sectional view showing the details of the structure illustrated in FIG. 17.

FIG. 20 is a flow diagram illustrating how our apparatus is used to make producer gas or synthesis gas.

FIG. 21 is a flow diagram illustrating how our apparatus is used to pyrolize coal, retort shale, or flame crack oil.

For an understanding fo the fundamental concepts of our invention, it is useful to consider first the simplified diagrammatic representation of our apparatus shown in FIG. 1. The apparatus 10 includes a reaction chamber 21 which is a metallic cylinder symmetrical about the longitudinal axis Z and defining a cylindrical reaction zone 22. The reaction chamber has an inlet end 23 through which oxidizer gas, such as air, may be injected axially into the reaction zone 22. Downstream from end 23 is an injection duct 24 through which oxidizer gas may be injected tangentially into the reaction zone 22. As mentioned earlier and discussed in more detail later, optimum combustion of some fuels requires air or other oxidizer gas to be injected both axially and tangentially into the reaction chamber. On the other hand, optimum combustion for many fuels, particularly coal requires only tangential injection of oxidizer into the reaction chamber.

A fuel injection pintle valve 25, aligned coaxially with the chamber 21 at its inlet end 23, includes a pintle 27 adapted for longitudinal adjustment within a fuel input tube 29 through which fuel flows into the reaction chamber. Pintle 27 has a tapered end portion 31 for deflecting the fuel radially outward from the longitudinal axis in a bell-shaped dispersion envelope 41. When the pintle is moved to the left, as shown in FIG. 1, the tapered surface of end portion 31 moves toward a valve seat 33 at the end of tube 29 to reduce gradually the rate at which fuel flows into the reaction zone 22. By this arrangement, pintle valve 25 variably controls the input fuel mass flow rate. At its right-hand end, the reaction chamber 21 includes a baffle 35 having a central aperture 37 through which gaseous reaction products generated in reaction zone 22, exit from the chamber. The baffle 35 separates particulate matter and slag droplets from the gaseous reaction products so that the stream passing out through aperture 37 is relatively free of liquid slag and solid particles.

As shown in FIGS. 2a-2c, carbonaceous fuel, for example, pulverized coal, is fed into the reaction chamber 21 in the form of a dense phase mixture with a carrier gas such as nitrogen (N.sub.2), compressed air or gaseous fuel. The tangentially injected airstream 47 thoroughly intermixes with the fuel and with the axial airstream, if axial air is utilized, and accelerates the burning solid fuel particles and reaction products in accordance with fluid flow principles discussed in greater detail hereinafter. The tangential air accelerates the fuel particles and reaction products in a manner to establish high velocity helical flow of the air, fuel particles, and reaction products within an annular region R.sub.1 of the reaction zone 22 adjacent the wall of the reaction chamber 21 and along a helical path 49 to the downstream end of the reaction zone. Fuel is injected into the reaction zone 22 through the pintle valve 25, which is located near the center of the inlet 23 of the reaction chamber 21. The mass flow rates of the fuel and air to the reaction zone are regulated in a manner to (a) maintain a relatively oxygen-rich stoichiometry within the annular flow region R.sub.1 and a relatively fuel-rich stoichiometry within the longitudinally extending central region R.sub.2 of the reaction chamber, and (b) provide high velocity helical flow of air, fuel particles, and combustion products through the reaction zone 22 with throughput residence times on the order of a few hundred milliseconds or less and stoichiometric conditions within predetermined ranges such that most of the carbon in the fuel particles is oxidized before they are centrifuged to the walls of or exit from the reaction chamber and most of the non-combustibles in the fuel are fused and centrifugally deposited as liquid slag on the walls, thereby being separated from the reaction products before they exit from the chamber.

At the downstream end of the reaction chamber, the gaseous reaction products are forced inwardly by the baffle 35 and exit from the chamber 21 through the central aperture 37. As the reaction products are forced inwardly by baffle 35, the angular velocity increases sharply in the region closely adjacent to the baffle so that remaining slag droplets are centrifuged out of the gas stream and are deposited, for the most part, on the walls of the chamber and the inside surface of baffle 35.

Particles in the bell-shaped dispersion envelope 41 move longitudinally through the chamber at an average velocity determined by the combined mass flow rates of air and fuel. Small particles tend to be caught up and carried with the mixture stream. Larger particles tend to follow trajectories determined in part by their original velocity vectors. Although large particles are accelerated by the rapidly rotating gases, they are accelerated to a lesser extent than smaller particles. Thus, as shown in FIG. 1, line 43 represents the outer boundary of the helical trajectories of relatively large fuel particles, for example, particles having initial diameters of about 200 microns. Such large particles do not in fact follow the line 43 but rather travel helically about the longitudinal axis within the envelope 41 of which the outer limit is indicated by line 43. Similarly, relatively small particles, for example, coal particles of about twenty micron initial diameter, travel in helical paths within the envelope 41, the inside limit of which is indicated by line 45. Of course, the flow patterns are, in actuality, far more complex than this diagrammatic illustration of the concepts: The shape of envelope 41 is not exact and varies as a function of time and scale. In addition, it should be understood that coal particles having initial diameters of, say, 20 microns become slag droplets of about 10 microns. Also, while we have described the first reaction zone as having a core portion (relatively fuel-rich) and an annular portion surrounding the core portion, it should be understood that these portions are neither sharply delineated nor time invariant. There are turbulences and eddies that change as a function of time. But it is correct to say that over a period to at least tens of minutes the core portion inside lines 45 (FIG. 1) is relatively very fule-rich as compared to the annular portion surrounding that core portion. Thus, substantially all fuel particles in the size range from about twenty microns to about 200 microns initial diameter follow helical trajectories within the envelope 41 between lines 43 and 45. Mixing of the fuel with the incoming tangential airstream is accompanied by momentum interchange and the formation of a mixture stream which extends as a substantially cylindrical helix along the length of the chamber.

The bell-shaped dispersion envelope 41, as shown in FIG. 1, is based on assumed injection of tangential air with flow velocities of 160 feet per second for the tangential air, about 50 feet per second for the axial air, and about 10 to 50 feet per second for the injected carrier gas and fuel mixture. It will be understood that the present invention is not limited to those specific velocity values or even to the ratios implied by those values. By selection of the optimum velocities and mass flow rates of tangential air, axial air, and fuel into the reaction chamber, the shape of the envelope 41 may be adjusted over a wide range. Such selection will depend on the particular fuel being used and other characteristics desired in the specific process. Optimum combustion of most carbonaceous fuels, particularly coal, is achieved with only tangential air injection into the reaction zone 22 through the tangential inlet 24.

In most embodiments and uses, it is desirable to operate the combustion apparatus with an overall fuel-rich or reducing atmosphere in the reaction zone 22. For example, fuel-rich operation is desirable to reduce reaction temperatures, minimize NO.sub.x, and limit slag vaporization as will be subsequently discussed.

In order to have a relatively compact reactor, it is necessary that the fuel particles be relatively small. In general, the fuel particles should be less than about 750 microns in diameter and preferably less than about 75 microns in diameter. Such small particles will burn within a few milliseconds. Our reactor is designed so that the swirling gases generate sufficient centrifugal force so that the particles move to the interior wall of the chamber but are essentailly all completely burned prior to impinging against the chamber wall. For example, a particle having a diameter of 75 microns burns within about 60 milliseconds. The aeroballistic environment into which this particle is injected preferably is controlled so that the forces acting on the particle will not move it to the wall prior to complete combustion.

It is generally understood that small particles are affected by aerodynamic drag forces to a greater extent than large particles. For example, when a small particle enters the swirling gases in the reaction zone, the oxidizer gas rushing by the particle creates a drag force which almost instantaneously changes the speed and direction of the small particle so that it coincides with the speed and direction of the swirling gases. In contrast, the inertia of a very large particle tends to keep this particle moving at the speed and direction at which it entered the swirling gas. For the small particles which we use almost all the particles attain the velocity of the swirling gases within a few milliseconds after entering the reaction zone.

As these particles swirl in the gases, a centrifugal force is generated which is directly proportional to the mass of the particle and the angular velocity of the particle. Larger particles have greater centrifugal forces acting on them than smaller particles and the effect of the drag force is less. Consequently, large particles tend to move more rapidly to the exterial wall than the smaller particles. By controlling the tangential velocity of the swirling gases, one controls the centrifugal and drag forces acting on the particles. This enables one to select the suitable tangential velocity of the swirling gases so that the large particles are burned before they impinge against the wall of the reaction chamber. The interaction of the incoming gases provides a vehicle by which we may vary the centrifugal and drag forces acting on the particles. By controlling the ratio of mass flow rates of the fuel and air streams, we are able to insure that essentially all the particles will burn before they strike the chamber wall. Moreover, the more wheel-like the flow of gases within the reaction zone, the greater will be the flight time of the particulates in the chamber.

In designing the reaction chamber, it is desirable to maximize the amount of slag that is captured in this chamber. Since small particles do not move to the wall as quickly as large particles, very small particles will escape through the aperture of the chamber, and there is always a certain loss of very minute slag droplets. However, chamber length and aperture opening are selected so that at least approximately 90 to 95% of the slag is captured within the chamber.

Care is taken not to inject the fuel particles with a velocity so great that the momentum of the particle would carry it to the chamber wall prior to burning. In other words, the velocity of the fuel particle must be sufficiently less than the velocity of the swirling gases so that the gases will act on the incoming particles and capture them in the swirl for a sufficient length of time to insure complete combustion.

Full appreciation of the characteristics of the wheel-type flow employed in our invention requires a detailed consideration of the gas flow and forces generated by the gases that act on the fuel particles.

There are two types of gas flows in the swirling gases in the reaction zone: vortex flow and wheel flow. In a theoretically pure vortex flow, the tangential velocity decreases as a function of radial position. In other words, the maximum tangential velocity is near the center of the rotating flow field. Vortex flow is mathematically characterized by the expression: ##EQU1## Where

V.sub.t =tangential velocity,

R.sub.o =radius of the chamber,

R=position of reference on radius, and

V.sub.o =tangential velocity at the outer radius.

Theoretically pure vortex flow is graphically illustrated in FIG. 3, where curve 51 is a plot of tangential velocity as a function of radial distance from the axis of rotation in a vortex flow field. As shown by curve 51, tangential velocity increases exponentially with decreasing radial position and, if pure vortex flow were maintained, would be extremely high near the axis.

In wheel flow, the entire fluid body spins together like a solid body. This type of flow we refer to as "pure wheel flow." Pure wheel flow is mathematically characterized by the expression:

Where

V.sub.t =tangential velocity,

R=position reference in the radial direction, and

.omega.=angular velocity at R.

Thus, in wheel flow the tangential velocity of the gas at any given radial position R is directly proportional to its radial position from the rotational axis. This is, of course, the distinguishing characteristic of a rotating solid body whose components are fixed in relation to each other. The angular velocity, .omega., is the same for all radial positions. Thus, in pure wheel flow .omega. is a constant for all points (positions) in the same cross section, with maximum tangential velocity occurring at the outer radius, as contrasted to pure vortex flows where the maximum tangential velocity is close to the axis. Pure wheel flow is illustrated in FIG. 4 where line 53 represents tangential velocity plotted as a function of radial distance from the rotational axis Z.

In mixing the tangential air entering the reaction chamber 21 with the axial air and/or fuel/carrier gas mixture entering the inlet end of the chamber, the flow of gas in the reaction zone 22 may be controlled so that is corresponds substantially to the velocity profile illustrated by curve 55 in FIG. 5. This curve is illustrative of one embodiment of the flow regime in the reaction zone 22. Curve portion 56 shows the region where velocity increases substantially as a linear function of radial distance from the axis of rotation and corresponds to pure wheel flow. The portion of the flow field more nearly corresponding to pure vortex flow is indicated by curve portion 57. In this combined wheel-vortex flow, the tangential velocity near the axis increases substantially linearly with distance from the axis to a maximum velocity at a distance approximately equal to the radius of the baffle aperture 37. Outwardly beyond that point, the velocity changes approximately inversely as the distance from the axis, and more nearly corresponds to vortex flow as discussed above and illustrated in FIG. 3. Thus, the flow field used approximates pure wheel flow in a core region of the combustion zone, has a transitional portion indicated at a, in FIGS. 3 and 4, and is substantially similar to vortex flow in an outer annular shell portion or region of the flow field.

The flight time of larger particles can be significantly increased by minimizing the tangential velocity of gases encountered early in their flight through the chamber. Thus, it is desirable that the core region from R=O to R=a should be as large in diameter as practically feasible. The actual diameter of the wheel-flow core region will vary along the length of the chamber and, near the downstream end, tends to be approximately equal to the radius of the baffle aperture 37. In upstream portions of the combustion zone the radius "a" of the wheel-flow core region can be maximized by controlling velocities, mass flow rates, and the fuel injection mode to thereby make the core region as large as possible consistent with capture of slag.

In accordance wth our invention, by regulating the velocities and mass flow rates of the air and fuel streams entering the reaction chamber 21, we can control momentum transfer between the air and the fuel, so that the flow field in reaction zone 22 is similar to the wheel-vortex flow illustrated by FIG. 5, and therefore, long flight times for particles are realized. As a result in a chamber as small as 18 inch diameter, we relaize flight times for large particles of the order 30 to 70 milliseconds. This aeroballistic control of chemical reaction in free flight is exploited to minimize loss of unburned fuel in the slag and to limit the amount of slag exiting the reaction chamber through aperture 37. This may also be enhanced by injecting fuel with a velocity less than that of the incoming tangential stream of oxidizer gas and causing the fuel to intercept those portions of the oxidizer gas stream which are tending toward higher angular velocity.

The significant difference between the two flows is residence times of particles in the reaction zone 22. For like particles injected at the same radii in the two types of flows, the stay time is much longer in the wheel flow than in the vortex flow. Thus, to provide a longer in-flight time, we prefer to operate under conditions which favor the establishment of a quasi wheel-type flow in the reaction zone 22. This enables us to achieve increased power densities. For example, a conventional Lurgi gasifier operated at 20 atmospheres pressure has a power density of 10 pounds of coal per hour per cubic foot of reaction chamber. Our apparatus operated at the same pressure will have a power density of about 1000 pounds of coal per hour per cubic foot of reaction chamber.

The advantage of maintaining a predominately wheel-type flow in our apparatus are best appreciated by considering the aerodynamics of the particle carried in the swirling gases. To reiterate, our primary objective is to suspend large particles for a flight time of sufficient duration so that they will be substantially completely reacted and reduced to slag droplets before impinging the walls of the reaction chamber. The apparatus and its operation are designed to minimize radial acceleration of unburned and partially-burned particles while assuring that most of the slag droplets will reach the walls. How this is achieved is best understood by considering particles in the reaction zone.

Consider a particle entering the reaction zone. Only drag forces act on this particle initially. Assuming a sperical particle, the drag force (F.sub.d) is ##EQU2## where

C.sub.d is the drag coefficient,

.rho..sub.g is the gas density,

D.sub.p is the particle diameter,

V.sub.g is the velocity of the gas,

V.sub.p is the velocity of the particle,

g is the acceleration of gravity.

Small particles, however, because they are light weight, i.e., have a low mass, are more affected by the drag force exerted on them by the swirling gases than larger, heavier particles. Since most of the particles we employ are relatively small, almost all these particles due to the drag forces acting on them will attain the same velocity of the swirling gases almost instantaneously.

With the particles rotating, centrifugal force (F.sub.c) is exerted on the particles. From basic physics

where

M is particle mass,

R is the radial position of the particle, and

.omega. is the angular velocity of the particle.

From this equation, one can see that the more massive a particle the greater will be the centrifugal force urging the particle toward the inner wall of the chamber. We control the angular velocity so that the centrifugal force is not so great that the velocity imparted to the particles carry them to the chamber wall prior to complete combustion. In a vortex-type flow, with high velocities near the center of the chamber, any fuel particle injected into the rotating stream will be subjected initially to a large centrifugal force and thereby be accelerated rapidly in the radial direction. On the other hand, in wheel flow, under identical injection conditions, the same particle experiences relatively low centrifugal force and, hence, it experiences low initial acceleration in the radial direction. Because the drag force primarily controls the movement of very small particles, these particles tend to stay in the same position in the gases once they are spun up and only move slowly towards the chamber wall.

It can be shown that a particle's tangential acceleration (dV)/(dt) is given by the expression ##EQU3## Note that particle acceleration is inversely proportional to the square of the particle diameter. Hence, small particles will attain the same velocity of the swirling gas more rapidly than larger particles, and tend not to move relative to surrounding gases to the same degree as large particles which tend to move into different gas environments as they travel and are thus continuously scrubbed by fresh oxidizer gases. This prevents developing a blanket of reaction products around large particles and thereby significantly enhances large particle combustion. The extent to which these advantages are realized in practice depends in part on the degree to which the flow field approximates pure wheel-flow.

FIG. 6 depicts the behavior of a given size particle in three different flow fields. The radial position of a 75 micron diameter particle in a nominally 1-1/2 foot diameter chamber is studied under three different conditions. Curve A shows that in pure vortex flow the particles would reach the chamber wall in about 10 milliseconds. Curve B shows that in a combined wheel-vortex flow field this particle reaches the wall in about 30 milliseconds. Curve C shows that in a pure wheel flow field the particle reaches the wall in excess of 70 milliseconds. Since the burn time of this particle is greater than 10 milliseconds, pure vortex flow will fail to achieve the result we desire. As the flow field more nearly approximates pure wheel flow, larger particles may be burned in this size chamber. The chamber size could be increased to attain in-flight burning of the particles in vortex flow, but this would impose an economic disadvantage and impair power density and efficiency.

Volume or in-flight burning, achieved as described above, provides relatively very high thermal efficiency in that it avoids burning on the wall, concomitant loss of carbon in the slag, and excessive loss of heat to the walls. In addition, wall burning would require the use of excess air which would reduce thermal efficiency and preclude maintenance of a reducing atmosphere in the center region R.sub.2 of the reaction zone 22 as discussed below. Moreover, by providing longer residence time for a given chamber diameter than that possible with straight flow through and enhanced in-flight "scrubbing" of larger particles, we are able to achieve relatively very high power densities. Because our apparatus maximizes the relative velocity between the rotating gases and larger particles, burning of large particles is enhances so that reaction zone 22 may be operated fuel-rich within its central region R.sub.2 without excessive deposition of unburned particles on the reaction chamber walls. The ability to operate fuel-rich makes it feasible to hold the reaction zone operating temperatures at temperature ranges which avoid excessive volatilization of slag and excessive production of nitrogen oxides. Hence, in our apparatus, up to 90% or more of the slag content of input fuel may be removed as a liquid before the gaseous reaction products leave the chamber.

According to the present invention the mass flow rates of the solid fuel and oxidizer gas or air is regulated to achieve two important results. These results are (i) high velocity helical flow of oxidizer gas or air and combustion products through the reaction zone 22 within residence times of the order of a few hundred milliseconds or less, and (ii) combustion temperatures and stoichiometric conditions in the regions R.sub.1, R.sub.2 within predetermined ranges such that most of the carbon contained in the fuel is oxidized before the fuel particles reach the wall of or exit from the reaction chamber 21, and most of the non-combustibles present in the fuel are fused and deposited on the chamber walls, as liquid slag, so as to be separated from the gaseous combustion products before they exit from the reaction zone.

The illustrated combustion apparatus is shown to have both axial and tangential oxidizer or air inlets since optimum combustion of some fuels requires both axial and tangential air. On the other hand, optimum combustion of many fuels, such as powdered or pulverized coal, requires only tangential air in addition to the fuel, of course. When burning these latter fuels, the axial air flow preferably is totally cut off.

FIGS. 7 and 8 illustrate an embodiment of our invention especially designed and adapted for the combustion of pulverized coal to generate a high temperature plasma stream for driving magnetohydrodynamic electric generators. In addition to the components heretofore described in connection with FIG. 1, the apparatus includes an oxidizer manifold 61 through which air from source 65 flows through secondary air duct 24 to injection port 58, and tangentially into the reaction zone 22.

As best shown in FIG. 8, pintle valve 25 receives fuel (i.e. a dense phase fuel/carrier fluid mixture) from a fuel source 63 with the fuel flowing through inlet tube 29 and being deflected radially outward from pintle end portion 31. Longitudinal adjustability of the pintle is provided by an externally threaded pintle sleeve 28 carried on the pintle and rotatively supported within an internally threaded bore.

The fuel source 63 preferably is a separate fuel mixing and dense phase transport apparatus illustrated in FIGS. 13 and 14 and described in more particular detail hereinafter. The essential function of source 63 is to provide pulverized coal entrained in a flow of carrier fluid with the coal-to-fluid mass ratio being controllable over a range from 0:1 to 100:1. The entrained flow of pulverized coal mixed with carrier fluid has flow characteristics similar to those of a viscous fluid and, as the entrained flow is dispersed through the pintle valve 25, the finely divided coal is sprayed therefrom as shown by the bell-shaped dispersion envelope 41 of FIG. 1.

In FIGS. 7 and 8, high temperature compressed air from oxidizer source 65 is fed through manifold 61 to provide first, second, and third streams of air to the apparatus. Manifold 61 includes main duct 66 extending from source 65 substantially parallel to the longitudinal axis of the combustion chamber 21, and a first branch duct 67 extending perpendicularly toward the chamber 21 and feeding high pressure primary air into a plenum 69 from which it passes through a multi-aperture flow straightening device 70. This primary air passes into the reaction zone 22 in a direction substantially parallel to the longitudinal axis of the chamber 21 and through the annular space surrounding the pintle valve 25. In plenum 69 volumetric expansion slows the air velocity and it is directed by the plenum walls to flow through the flow straightening device 70. As best shown in FIGS. 8 and 9, device 70 is a freestanding assembly of silicon-carbide vanes fitting together to form a multi-aperture assembly through which the primary airstream passes. Alternatively, the vanes may be fabricated of Inconel 800 or another corrosion resistant, high temperature alloy consistent with an overall design scheme employing all-metal construction. In such cases the vanes may be water-cooled by means of conventional cooling technique.

Secondary air input is furnished from source 65 by way of main air duct 66 and branch duct 24 to the tangentially aligned air injection port 59 at a velocity sufficient to establish within the reaction zone 22, a rotating mixture consisting of fuel particles, primary air, and secondary air. To maintain the desired aeroballistic conditions in the reaction zone and to regulate reaction temperatures, it is desirable or essential to control the relative flow values of primary and secondary air, the mass flow rate of air relative to the input fuel, and in most cases to be totally cut off the primary air so that only tangential air enters the reaction chamber. To accomplish such parametric regulation, conventional fluid valves (not shown) may be used in air ducts 67 and 24 for preselecting or continuously regulating the respective mass flow rates.

Control of slagging, so that substantially all the slag content of the fuel is deposited on the walls of the combustion chamber, is a feature of considerable importance. Optimized separation of slag from the gaseous reaction products is achieved first by establishing and controlling a quasi wheel-type flow field in the reaction zone 22, and secondly by regulating reaction temperature so that slag volatilization and NO.sub.x production are minimized. Temperature control is achieved by regulating the temperature of the input air and selectively modifying the air-to-fuel ratio so that a relatively fuel-rich stoichiometry is sustained within the center region R.sub.2 of the reaction zone. This provides fuel-rich combustion and results in a significant portion of the carbon contained in the coal leaving the reaction zone 22 as carbon monoxide, limits the generation of thermal energy in the reaction zone, and thereby controls the operating temperature within reaction chamber 21. Temperature control taken together with centrifugal acceleration of slag particles toward the walls of chamber 21 enables the removal of up to 90% or more of the slag from the stream of gaseous reaction products before such products exit from the reaction zone through the central aperture 37 of baffle 35.

If inner surface 71 of the combustion chamber were coated with a refractory ceramic material, the erosive effects of the slag, high velocity flow, and burning fuel particles within the reaction zone would tend to strip the refractory from the walls of the chamber 21 and, once that has occurred, begin to attack the metal inner surface 71 of the chamber. We avoid this difficulty by forming a protective layer of solidified slag deposited upon surface 71 thereby limiting further attack. To that end, metal coolant conduits 73 are provided on the inner surface of the chamber 21. Conduits 73 form a water-cooled lining for the reaction chamber 21 which retains and solidifies enough slag to form a protective slag layer having a relatively low-thermal conductivity. Conventional arrangements are used for feeding coolant to the conduits 73, i.e., manifolds 74 and 75.

As shown best in FIGS. 7, 8, and 10, baffle 35 is an annular plate having a double-coil of coolant conduit 77 disposed on its surface and positioned substantially normal to the longitudinal axis at the downstream end of chamber 21. One function of baffle 35 is to stop slag droplets which have not yet reached the walls of the chamber 21 and thereby minimize the slag and ash content of the gaseous reaction products exiting from the chamber. In addition, the rotating stream of gaseous reaction products, upon arriving at the downstream end of the chamber, is forced by a baffle 35 to move radially inward, toward aperture 37. As the high velocity rotating gas stream is forced inwardly, the angular velocity increases by a factor of 3 or 4 or more. This sharp increase in centrifugal forces results in substantially all of the slag content of the fuel being centrifuged out of the gaseous reaction products and deposited as a liquid slag layer on the inner surface 71 of the combustion chamber and on the baffle 35.

The liquid slag flows in response to aerodynamic drag and gravity toward the bottom of the reaction chamber, through slagging port 78, and out to a slag trap 79 at the bottom of the chamber. As best shown in FIGS. 8 and 10, the short section of cylindrical conduit which defines slagging port 78 is cooled by cooling water flowing through a conventional water jacket having inlet 80 and outlet 81. In the region of the slagging port 78, the coolant conduits 73 are formed to provide a shaped inner-surface portion 82 defining a substantial aperture between the adjacent conduits 73 at the location of the slagging port 78. The slag-dumping subsystem preferably includes a pressurized slag reservoir (not shown) to prevent the escape of gaseous reaction products through the slagging port.

In its application to magnetohydrodynamics, our apparatus additionally includes a secondary reaction chamber 85 coupled to the downstream end of chamber 21 and defining a second reaction zone 88. Secondary chamber 85 receives gaseous reaction products from chamber 21 and modifies the high temperature gaseous reaction products to produce at its output 87 a high velocity plasma suitable for injection into the plasma channel of a magnetohydrodynamic (MHD) electric power generating device. Such MHD systems form no part of the present invention, are well known in the prior art, and are not further described herein.

Gaseous reaction products passing out of reaction zone 22 through aperture 37 pass into the second reaction zone 88. Immediately downstream from baffle 35, we provide a reactant injection assembly 90 for injecting into the high temperature gas stream selected chemical reactants such as, for example, potassium carbonate. Injector assembly 90 includes a reactant input tube 91 which extends transaxially of chamber 85 and is supported coaxially with a coolant conduit 92. Mounted on reactant tube 91 and substantially at the axis of chamber 85 is a reactant injector comprising a sleeve 94, having a pintle 95 supported coaxially therein. This coaxial pintle reactant injector preferably is a miniature version of the coaxial pintle valve 25 heretofore described and shown in FIGS. 1 and 8. For efficient performance of magnetohydrodynamic channel have electrical characteristics corresponding to those of a highly conductive fluid. Thus in the magnetohydrodynamic application of our invention, it is preferred that the gas stream 87 exiting from reaction chamber 88 be substantially completely and uniformly ionized. Injection of potassium carbonate assures complete and uniform ionization of the reaction products as they pass through reaction zone 88. In other applications of our apparatus, the reactant injection assembly 90 may be employed for injecting substantially any additive or chemical reactant into the swirling gas stream as it passes through aperture 37 into reaction zone 88.

Immediately downstream from the reactant injector 93, the second chamber 85 is provided with an arrangement for injecting a volume of preheated air necessary to complete stoichiometric reaction. This tertiary air is injected with a sufficient tangential velocity component to null out, by momentum interchange, the angular velocity of the gaseous reaction products received from aperture 37. More specifically, this second stage deswirl subsystem comprises tangentially extending air duct 96 receiving high temperature air from manifold 61 and transporting the same into toroidal air distributor 97 which, as best shown in FIGS. 8 and 12, extends circumferentially around the second chamber 85 and has, at its inner periphery, twelve air injection ports 98 for introducing high velocity tangential airstreams from the distributor 97 into reaction zone 88. In using our apparatus as the plasma source for a magnetohydrodynamic power system, it is desirable that the output plasma stream have substantially no angular velocity. To that end, regulation of the air flow through duct 96 and distributor 97 may be used to reduce to zero the angular velocity of the gas stream within chamber 85. Alternatively, a deswirl chamber having its exhaust conduit disposed perpendicular to the longitudinal axis of the first combustion chamber may be used to achieve this result. For other applications in which angular velocity is irrelevant, volumetric control of the air supplied through duct 96 may be used for preselecting or continuously varying stoichiometry within reaction zone 88. As required, air manifold 61 and the several ducts extending therefrom are provided with external water-cooled jackets. Conventional manifolds are used for feeding coolant to the water jackets.

Pulverized fuel, e.g. coal, is transported from a ball mill or storage facility to the reaction chamber 21 in a dense phase mixture with carrier gas through a tubular conduit. Because reaction chamber 21 may operate at pressures in the range from about one to eight atmospheres or higher, the fuel transport subsystem preferably is pressurized to substantially the same level. FIGS. 13 and 14 illustrate the apparatus by which the pressurized dense phase fuel transport is implemented in accordance with a preferred embodiment of our invention. As shown in FIG. 13, the coal hopper 145 is filled with powdered coal normally pulverized to a fineness of the order of 200 mesh from a coal storage facility (not shown) through a fill hatch 146 located at the top of the domed portion 147. Filling of the pressurized coal hopper may be accomplished by means of an intermediate pressurizable transfer vessel (not shown) or, for example, by a conventional screw pump for handlng pulverized coal. In addition to the domed portion 147, the coal hopper comprises an intermediate cylindrical portion and a lower conical portion 148 having a 30.degree. included angle. At the base of conical portion 148, we provide a coal fluidizing injector 149 from which the pulverized coal flows through a throttling valve 150 to an eductor assembly 156 which operates to accelerate the coal particles to a velocity of about 20 feet per second and transport the coal, in a dense phase mixture with air or another suitable carrier gas through a coal feed line 158, for continuous injection into the reaction chamber 21 (FIGS. 7 and 8). It will be understood that the coal feed line 158 extends from the eductor assembly 156 and is connected to inlet tube 29 of pintle valve 25. Carrier gas for pressurizing the coal hopper 145 is supplied from gas source 152 over line 153 and through a control valve 154 to an input connection at the top of the hopper. Carrier gas is also supplied from the source 152 by way of a line 155 and a control valve 157 to the fluidizing injector 149. Compressed gas for energizing the eductor assembly 156 is fed from a gas source 159 through a control valve 160 to the input of the eductor. The fluidizing injector 149 and the eductor assembly 156 are illustrated in detail in FIG. 14, which is a cross section taken along the cylindrical axis of the fluidizing injector.

As shown in FIG. 14, the fluidizing injector 149 comprises a substantially cylindrical metallic member 166, having at its upper end a conical portion 167 and a planar flange of 170. Flange 170 is connected to and sealed to the bottom end of the conical portion 148 of the coal hopper. Member 166 has a 1/2-inch diameter central bore 172 extending vertically upward and opening into a conical aperture 174 which has a 45.degree. included angle between opposite walls 175 and is about six inches in diameter at its upper end. Intermediate the ends of conical aperture 174, and on the periphery of member 166, there is provided a circumferentially extending gas manifold 176. The gas manifold 175 is bonded to the surface of member 166 covering a circumferential groove 178 into which gas from the manifold is distributed. From groove 178, a plurality of equiangularly spaced holes 179 extend radially inward through the wall of member 166 to the conical aperture 174. Pressurized carrier gas from source 152 is fed through control valve 157 to the manifold 176 from which it is distributed and flows through the sixteen radial holes 179 into the conical aperture 174. This carrier gas injection fluidizes the pulverized coal contained within aperture 174 and propels a mixture of carrier gas and powdered fuel downwardly through central bore 172. From the base of member 166, the flowing mixture passes through throttling valve 150 and into a vertically extending bore 181 of eductor assembly 156. The fuel throttling valve 150 may be a conventional ball valve having its control shaft coupled to be rotated by a gear motor 183. Conventional circuitry is used to monitor and control the gear motor shaft position and thereby regulate the fuel flow through throttling valve 150 in accordance with the fuel to carrier gas volumetric or mass ratio desired.

The eductor assembly 156 comprises a housing 185 having a cylindrical bore 186 extending horizontally there through and a vertically extending bore 181 which connects with the horizontal bore 186 and through which the pressurized coal flows from throttling valve 150. A convergent nozzle 187 is secured within horizontal bore 186 by threads 188 and is operative for injecting high pressure carrier gas into the housing 185 wherein the gas jet impinges the downwardly flowing stream of pulverized coal and accelerates the same outwardly through a connector 189 and coal feed line 158. The inner end of connector 189 is provided with a conical bore 190 which funnels the mixture of pulverized fuel and carrier gas into feed line 158. The convergent nozzle 187 is coupled to and fed with compressed carrier gas from source 159 (FIG. 13) by way of control valve 160.

In operation, the fluidizing injector 149 contains, in conical aperture 174, a region of high turbulence wherein the pulverized coal is mechanically agitated and lubricated so that a smooth and reliable flow of coal and carrier gas move downwardly through central bore 172. The carrier gas infeed also balances the overhead pressure of the pressurized coal hopper 145 so that hopper pressure is maintained, even though the volume of coal contained in hopper 145 gradually decreases. In the preferred method of operation, the fluidizing injector provides a fluidization volumetric flow rate equal to the volumetric flow rate of the coal plus any carrier gas lost under steady state running conditions.

When steady state coal flow has been established downwardly through throttling valve 150, the flowing coal is diluted and accelerated by the compressed carrier gas injected through convergent nozzle 187 in the eductor assembly. The converging internal bore of nozzle 187 provides a focused gas jet such that with the gas velocity and coal mass flow rate properly adjusted, the coal particles are accelerated to a velocity of about twenty feet per second and flow continuously at that velocity through feed line 158 to the reaction chamber 21.

The solid fuel is normally pulverized to a fineness of the order of 200 mesh; however, a range of sizes may be used. We have established that solids-to-gas ratios as high as about 100:1 are feasible. With fluidizing (N.sub.2) pressures ranging from 10 to 80 pounds per square inch, we have achieved ratios of the order of 50:1 while maintaining relatively uniform flow rates. After the coal dust is loosened by fluidizing through the fluidization injector 149 for several minutes, the carrier gas input to the fluidization injector may be turned off and the dense phase coal transport continued simply by maintaining pressurization of the coal hopper 145 and compressed gas feed to the eductor assembly 156. The solids-to-gas ratio and the transport velocity in feed line 158 may be continuously controlled or alternatively set at any preselected value within the above ranges by controlling the coal throttling valve 150 and gas feed valve 160. Conventional circuitry including flow rate transducers are used for monitoring these operational parameters and providing feedback signals to energize control motor 183 and thereby regulate valve 150, as well as controlling input air velocity and pressure.

While we nominally use dry nitrogen or air as the fluidizing carrier gas it is to be understood that substantially any liquid or gas, including petroleum liquids, water, and hydrocarbon gases may be employed.

In the operation of our apparatus as a power source for driving magnetohydrodynamic generators, finely divided coal which has been processed to the 100-200 mesh level is entrained in a flow of near ambient temperature air. For applications requiring minimal enthalpic loss such as plasma generation, the mass ratio of solid fuel particles to ambient air carrier is in the range of 30-100:1. The dense phase fuel transport limits the amount of relatively cold air introduced into the combustion zone 22 and thereby aids in maximizing the output plasma temperature levels. The entrained flow of coal particles is fed through the pintle valve 25 and is directed radially outwardly into combustion zone 22, in the bell-shaped dispersion pattern 41 (FIG. 1).

The oxidizer utilized in plasma generation is generally preheated air at appoximately 2900.degree. F. This preheated air may be provided with "make-up" oxygen prior to introduction to the combustion zone if required by the specific nature of the coal fuel being utilized. A helical wheel-type flow of preheated air is established within combustion zone 22, and the entrained flow of coal in carrier gas is directed into the wheel-type flow. To hold combustion temperatures below the slag volatilization temperature, combustion zone 22 preferably is operated fuel-rich in the range of about 0.4-0.9 of the stoichiometric amount of oxidizer. This produces temperatures in zone 22 ranging from 3000.degree. F. to 3800.degree. F., depending on the composition of the slag. The high temperature gaseous combustion products exit from combustion zone 22 through central aperture 37 of baffle 35 at a temperature of approximately 3400.degree. F. These gases from the fuel-rich atmosphere within combustion zone 22 will contain slag droplets smaller than approximately 10 microns diameter, as well as a modest amount of volatilized slag.

As previously described, additional oxidizer required to bring the gaseous combustion products to stoichiometry and complete combustion is introduced into second chamber 85 through input duct 96 and distributor 97. Completing the combustion of CO and H.sub.2 in reaction zone 88 increases the temperature level of the gas stream from approximately 3400.degree. F. to approximately 5100.degree. F. at outlet 87. Outlet 87 may be connected directly to a magnetohydrodynamic generator or other system for the utilization of thermal and/or gas-kinetic energy. Slag droplets, ash, and fuel particles which are not burned or captured on the walls of chamber 21 are relatively very small. Hence, for the most part, they are gasified upon being exposed to the higher temperature regime within reaction zone 88.

In the previously described preferred embodiment of our apparatus, pintle valve 25 is aligned with and positioned substantially on the longitudinal axis of combustion chamber 21. While that coaxial symmetry has certain advantages, it should be understood that our invention is not so limited. In alternative embodiments of our invention, the pintle valve 25 may be spaced from the longitudinal axis and/or positioned with inlet tube 29 at substantially any angle relative to the longitudinal axis of chamber 21.

In various applications of our invention it may be desirable to modify the bell-shaped fuel distribution envelope 41 (FIG. 1) by injecting pulverized fuel throughout only a limited angular segment of the pattern. FIGS. 15 and 16 show a modified pintle valve used for creating a fuel dispersion pattern corresponding to an angular segment of the bell-shaped envelope 41. This modified pintle valve 225 includes a fuel inlet tube 229 substantially identical to the inlet tube 29 of the valve shown in FIG. 8. At an input end 230, a stream of carbonaceous fuel mixed with a carrier gas flows into the pintle valve 225 through the interspace between 229 and the centrally aligned pintle 227. At its right-hand end as shown in FIG. 15, the pintle carries an enlarged circular end portion 231 having a tapered surface 232 which seals against valve seat 233 when pintle 227 is moved longitudinally toward the left. In this embodiment, the pintle valve 225 differs in that circular end portion 231 includes a thin walled cylindrical skirt 234 formed integrally with end portion 231 and extending toward the input end of tube 229 closely adjacent to the inside wall of the inlet tube. As indicted at 235, the skirt 234 has a portion cut away closely adjacent end portion 231 to form an aperture 236 which extends circumferentially of the skirt 234 through an angle corresponding to the angular extent of the fan-shaped fuel distribution pattern desired. For example, aperture 236 may extend through an included angle of about 60.degree.. In this embodiment the pintle shaft 227 may be slidably supported for motion longitudinally of the inlet tube 229 without rotating. When the pintle shaft 227 is moved to its closed position (as shown in FIG. 15) tapered portion 232 seals against valve seat 233 throughout its periphery and thereby reduces the flow of fuel and carrier gas substantially at zero. When the pintle is moved to its fully opened position as shown in FIG. 16 skirt 234 maintains a sliding seal against the inner wall of inlet tube 229, thereby precluding the outflow of fuel and carrier gas except in the region of aperture 236. Thus, as shown in FIG. 16, the pressurized stream of fuel and carrier gas flowing through inlet tube 229 passes out through aperture 236 and is sprayed into the combustion zone throughout a limited angular-segment pattern corresponding to an angular portion of the bell-shaped envelope 41 of FIG. 1. As the pintle 227 is moved from the open position shown in FIG. 16 toward the closed position as shown in FIG. 15, the aperture 236 is incrementally closed off by valve seat 233 to gradually reduce the mass flow rate of fuel and carrier gas injected into the reaction chamber. While we have illustrated this segmented pintle valve as including the peripherally extending aperture 236, it will be understood that other equivalent structures, such as plurality of angularly spaced cylindrical holes, may be employed.

An alternative reaction chamber structure shown in FIGS. 17, 18, and 19, is advantageous for higher pressure applications. As shown in FIG. 17, the chamber 240 is a double wall structure having an outer wall 242 and an inner wall 243. Inner wall 243 has coolant passages 244 chemically milled on an outer surface thereof, as seen in FIG. 19. The coolant passages are closed by seam welding outer wall 242 to rib portions 246 between passages 244. The heat exchange sub-system receives coolant at inlet 248 of water manifold 249, distributes the coolant through passages 244, and exhausts the coolant through outlet manifold 250. The deposition of a layer of slag over metal inner surface 243 of the chamber reduces heat transfer to the coolant and thereby minimizes enthalpic loss from the stream of gaseous combustion products.

For a given combustion temperature, as determined by the regulation of relative input rates of fuel and oxidizer, the slag produced during combustion collects as a coating of a solidified slag over metal inner surface 243 of the chamber 240 until the thickness of the insulating layer of solidified slag is such that any slag subsequently deposited is substantially insulated from the cooling effect of the water in heat exchange passages 244. At that point, equilibrium between the solid and liquid phases of the slag is reached, and a flowing layer of liquid slag will cover the insulating layer of solidified slag. This layer of liquid slag flows, by gravity and aerodynamic forces, toward a lower portion of the combustion chamber where it is removed at a liquid slag trap 252. In FIG. 17, aperture 254 is the tangential oxidizer injection port corresponding to port 39 of FIGS. 7 and 8.

The apparatus 10 of our invention may be adapted to make producer gas in air under conditions which favor the formation of carbon monoxide. The producer gas from the apparatus 10 is forwarded to a conventional gas or oil fired burner and serves as fuel for the burner. Thus, our apparatus provides a means for burning coal to produce a gaseous fuel which can be used as a substitute for natural gas or oil.

The system illustrated in FIG. 21 schematically represents the way in which our apparatus is used to make producer gas. The coal combustor apparatus 10 is of the type previously described in which the particles of fuel are burned before they would strike the internal wall of the apparatus. Compressed air, preferably pre-heated, is fed through valved line 300 into the reaction chamber of the apparatus 10 in the swirling fashion previously described. Pulverized coal is injected through the pintle (not shown). In order to remove SO.sub.x from the reaction products, carbonates would be added to the reaction zone. By controlling the mass flow rates of the coal and air, the amount of carbon monoxide would be maximized. The combustible products would be carried in the exhaust gases optionally through a hot gas filter, to the gas or oil fired burner. Any slag particles exiting with the exhaust gases would be trapped in the filter and removed as waste. Slag would be withdrawn from the apparatus 10 and dumped at a suitable disposal site.

When it is desirable to provide a high-Btu synthesis gas, oxygen is used in place of air, and steam is injected into the reaction zone of apparatus 10. Consequently, there will be little nitrogen in the exhaust gases exiting the apparatus 10. In this event the valve 310 in line 300 would be closed and the valve 320 which controls the flow of oxygen from an oxygen source 322 would be opened. The mass flow rates of coal, oxygen, and steam would be controlled so that the desired amount of carbon monoxide and hydrogen would be produced in apparatus 10. The synthesis gas would then be forwarded through the hot gas filter to a chemical plant which would use the synthesis gas to produce the desired chemicals. In producing synthesis gas it would also be desirable to add carbonates to remove SO.sub.x from the exhaust gases.